A H2020 Research and Innovation Action project, Grant Agreement number 814985
D5.1 - Report on Best Available Technologies (BAT)
for central receiver systems
This deliverable report D5.1 is part of a project that has received funding from the European Union’s
Horizon 2020 research and innovation programme under Grant Agreement No. 814985
WP 5: Techno-economic, social and environmental assessments
Task 5.1: Techno-economic, social and environmental assessments
Version: 01 version, Thursday, 5th December 2019
Deliverable No. 5.1
Work Package WP5
Lead beneﬁciary Abengoa Energia
Contributing beneﬁciary(ies) University of Seville
Due date of deliverable 30 November 2019
Actual submission date 5 December 2019
History of Changes
Version Date Changes
0.a 30/11/2019 Original version created by Abengoa Energia and USE
0.b 04/12/2019 Comments by Prof. Giampaolo Manzolini (Coordinator)
01 05/12/2019 Approved by Dr. Cristina Prieto (Abengoa Energia)
Table of Contents
Technical References 2
History of Changes 3
Table of Contents 4
1Executive Summary 6
2Fundamentals of CSP for STE 7
2.1 Introduction to CSP-STE Technologies . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 7
3Review of Solar Subsystems 10
3.1 SolarField ................................................ 10
3.2 Receiver.................................................. 14
3.2.1 GasReceiver ........................................... 15
3.2.2 LiquidReceiver.......................................... 16
3.2.3 SolidParticleReceiver...................................... 16
3.3 Thermal Energy Storage System . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 17
3.3.1 Storage based on steam accumulation . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 18
3.3.2 Storage based on molten salts . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 20
3.3.3 SteamGenerator......................................... 21
4Review of Power Block 22
4.1 Fundamentals of Rankine Cycles for Steam Turbines . . . . . . . . . . . . . . . . . . . . . . . . . 22
4.2 Power Block in a CSP-STE power plant . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 25
4.3 Auxiliary systems of the power block . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 27
4.4 Design and performance of the steam cycle . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 28
4.5 Transient operation mode and control strategies of the steam cycle . . . . . . . . . . . . . . . . . 28
4.6 Current development trends of steam cycles in CSP plants . . . . . . . . . . . . . . . . . . . . . . 29
5Techno-Economic Status of Solar Tower Plants 30
7Power Block based on supercritical CO2cycles 38
7.1 Origins of the supercritical CO2cycles................................. 38
7.2 Fundamentals of the supercritical CO2cycle and comparison against gas and steam cycles . . . . 39
7.3 Candidate sCO2cycles for CSP-STE applications . . . . . . . . . . . . . . . . . . . . . . . . . . . 41
7.4 Expected thermal performance of CSP-STE power plants based on sCO2cycles . . . . . . . . . . 45
7.4.1 Results .............................................. 45
7.4.2 ComparedAnalysis........................................ 47
7.5 Expected economic performance of CSP-STE power plants based on sCO2cycles . . . . . . . . . 49
7.5.1 Capitalcosts ........................................... 49
7.5.2 Capitalcostbreakdown ..................................... 51
7.5.3 Levelized Cost of Electricity . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 53
7.6 Projects under development worldwide . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 55
7.6.1 NorthAmerica .......................................... 55
7.6.2 Europe .............................................. 57
7.6.3 Restoftheworld......................................... 57
6Executive Summary6Executive Summary6Executive Summary
1 Executive Summary
The purpose of this document is to analyze the state-of-the-art of the CSP technology, focused on the solar
tower conﬁguration, and the possibility of integrating a supercritical CO2(sCO2) cycle to substitute the tradi-
tional steam cycle. To that end, the document is divided in six sections. The ﬁrst section presents a description
of the fundamentals of Concentrating Solar Power (CSP) technology for the production of solar thermal electric-
ity (STE). In the second section, a review of the solar subsystems is provided, describing the solar ﬁeld, receiver
and Thermal Energy Storage (TES) system. This second section incorporates a detailed description of all the key
components present in a CSP facility, familiarizing the reader with the current state of the art of the technology.
In the next section, the power block of the CSP plants is reviewed and the usual steam cycles used in contem-
porary CSP facilities are discussed. After this analysis, a description of the economics of state-of-the-art solar
tower plants is carried out, including a discussion about the expected cost reductions and market deployment
in the mid and long terms. A study of possible hybridization solutions is performed in the ﬁfth section, under a
decarbonization scenario. The last section scrutinizes the supercritical CO2technology, both its fundamentals
and a the potential application to CSP plants. This section approaches the technology from the technical and
economic standpoints, akin to the preceding sections about state-of-the-art CSP plants based on steam turbines.
Overall, this document provides an insightful review of the Best Available Technologies for CSP applicatons
that are either currently available or foreseen in the near future, along with the pathways to be followed in the
short term to improve the performance of this power generation technology.
Fundamentals of CSP for STE 7Fundamentals of CSP for STE 7Fundamentals of CSP for STE 7
2 Fundamentals of CSP for STE
2.1 Introduction to CSP-STE Technologies
The global energy demand will increase by more than a quarter by 2040, owing to the higher standards of
living overall and to the foreseen population growth, estimated at 1.7 billion, both of which eﬀects will be
more visible in developing countries . The current energy sources are carbon intensive, hence contributing
to increasing the concentration of carbon dioxide which represents over 70% of the greenhouse gas emissions
worldwide [1, 2, 3, 4] and is the largest contributor to climate change. To compensate for the latter eﬀect,
several renewable technologies, such as photovoltaic panels or wind technology, have experienced a noteworthy
development in recent years. Both technologies constitute a major source of aﬀordable, environmentally-friendly
electricity into the power generation landscape, but also bring about additional requirements for the reliable
operation of power systems, thus stressing the grid .
Concentrating solar power (CSP) technology, on the other hand, has the potential to provide cheap, CO2-
free electricity in locations with appropriate environmental conditions. Also, this technology allows for an easy
integration of thermal storage systems (TES) able to store the energy required to operate the power plant at
full capacity for up to 17 hours, hence enabling 24 hours of uninterrupted electric power generation. This ca-
pacity allows the system to tailor the production of electricity production to the instantaneous energy demand
[5, 6, 7, 8]. Power dispatchability is therefore a unique feature of CSP-STE, setting it apart from other renewable
energy sources like wind or solar-photovoltaic.
CSP-STE technologies are usually divided in four main categories, according to the conﬁguration of the
elements collecting and concentrating solar energy: linear Fresnel, parabolic dish, parabolic trough and solar
tower. This is shown in Figure 1(a). In parabolic trough and linear Fresnel systems, the mirrors track the
sun along one axis(line focus) whereas tracking has two degrees of freedom in solar towers and parabolic dish
systems (point focus). Also, the receiver remains ﬁxed in linear Fresnel and solar tower systems, while it changes
position in parabolic trough and parabolic dish systems . Among these technologies, only parabolic trough
and solar tower are deployed commercially at a relevant scale.
In parabolic trough technology, the energy of the sun is concentrated by a linear trough resulting from
a parabola extruded normal to its plane, and reﬂected onto a receiver tube running along the inner side of
the collector . The energy concentrated on the outer wall of the receiver is transferred to a heat transfer
ﬂuid (HTF), commonly synthetic oil, ﬂowing inside and this HTF eventually transfers this energy to the power
block where electricity is produced in a conventional steam turbine. Parabolic trough technology can also be
integrated with existing coal-ﬁred plants or combined cycles . Solar power towers convert solar power into
electricity using a large number of sun-tracking mirrors, also called heliostats (Figure 2), which focuse sunlight
on a receiver located atop a very high tower . The HTF that ﬂows inside the receiver (commonly molten
salts or water/steam), or the water/steam ﬂow in a direct steam generation embodiment, is heated by this
sunlight and then used directly or through a conventional steam generator in a steam cycle to produce elec-
tricity. Linear Fresnel technologies  use ﬂat or slightly curved mirrors mounted on trackers at ground level
and conﬁgured to reﬂect sunlight onto one or more receiver tubes located above the mirrors. A small parabolic
mirror is sometimes added atop the receiver to further concentrate the sunlight. Parabolic dish systems consist
of a parabolic-shaped point focus concentrator in the form of a dish that reﬂects solar radiation onto a receiver
located at the focal point . These concentrators are mounted on a structure with two degrees of freedom
which enable perfect tracking of the sun. The energy collected is typically used by a heat engine directly,
mounted on the receiver and moving with the dish structure. Stirling and Brayton cycle engines are the usual
prime-movers of choice for this applications .
8Fundamentals of CSP for STE8Fundamentals of CSP for STE8Fundamentals of CSP for STE
(a) Classiﬁcation of CSP technologies. (b) Combined eﬃciency vs. receiver temperature at diﬀerent
Figure 1: Solar technologies classiﬁcation and limits.
The concentration ratio of each collector type is tightly linked to the maximum temperature that can be
achieved at the receiver and, therefore, the maximum solar-to-electric conversion eﬃciency of the system. This
is shown in Figure 1(b) where the dependence of the combined eﬃciency of receiver and power block on receiver
temperature and concentration ratio becomes evident. For very high temperatures, the eﬃciency of the power
block increases but the heat losses from the receiver more than compensate this eﬀect, and the opposite is true
for very low reciver temperature. The only means of achieving high receiver and power block eﬃciencies at
higher temperature is increasing concentration ratio.
Linear technologies such as linear Fresnel and parabolic trough have concentration ratios lower than 100,
which limits their performance according to the foregoing statement. Linear Fresnel has even lower eﬃciency
than parabolic trough due to the losses inherent to the approximation of the true parabola by an array of
ﬂat mirrors. On the other hand, the concentration ratio of the parabolic dish is highest amongst the existing
technologies, reaching values close to ten thousand. The disadvantages of the parabolic dish technology is the
limited scale (due to the strong wind loads on the dish) and diﬃculty to enable Thermal Energy Storage. Ac-
cordingly, the parabolic dish technology ends up being a direct competitor of PV in the marketplace, but with
higher costs and no visible advantages .
Parabolic trough technology has low concentration ratios, but it is still deployed commercially worldwide
thanks to moderate capital costs and high technological maturity. The peak operating temperature is currently
limited to 400oC as this is the maximum temperature achieved by the heat transfer ﬂuids available. The in-
tegration of TES in parabolic trough technologies is easy, and it is commercially available using molten salts.
Yet, as said, the maximum temperature of the TES system is limited by the maximum operating temperatures
of the parabolic trough.
The concentration ratio of solar tower technologies lies between those of parabolic troughs and parabolic
dish, in the order of several thousands. The upper limit for this concentration is nonetheless not set by optics
but by receiver materials and HTF stability. Typical operating temperatures in the receiver of a solar tower
plant are 565oC, set by the HTF (molten salts when indirect steam generation is used) or the steam turbine (if
direct steam generation is used), with concentration ratios close to 1000. The solar tower technology is already
proven, with diﬀerent operational plants around the World. Moreover, the technology is still at the ﬁrst part
of the learning curve and thus strong cost reductions must be expected.
Fundamentals of CSP for STE 9Fundamentals of CSP for STE 9Fundamentals of CSP for STE 9
Linear Fresnel Parabolic trough Solar tower Parabolic dish
Concentration ratio 60 80 1000 5000
Maximum Temperature 200 400 600 1200
R&D status demonstration commercial early stage commercial commercial
Global plant eﬃciency 15 16 19 24 
Table 1: Comparison of CSP technologies.
In order to accommodate (i.e., to provide the necessary operating conditions for a meaningful integration
of) Supercritical CO2power cycles, the receiver temperature of a CSP-STE plant must reach ca. 700oC. Such
a high temperature can only be reached by point focusing technologies, in particular solar towers at the large
scale, as explained before and presented in Figure 1(b). This is the reason why SCARABEUS is focused on on
solar tower technology whilst the other collector types are disregarded.
10 Review of Solar Subsystems10 Review of Solar Subsystems10 Review of Solar Subsystems
3 Review of Solar Subsystems
3.1 Solar Field
The solar ﬁeld is responsible for collecting and concentrating the solar resource and for delivering it to the
receiver. Solar energy is a sparsely distributed resource which needs to be concentrated to enable the high
temperatures that are needed in a thermal power plant. Due to its scattering and low energy density, large
collection (aperturee) areas are necessary to collect the energy that is needed by a commercial-scale power cycle.
In solar tower technology, there are two main factors under consideration for the solar ﬁeld: the elements that
reﬂects the sunlight onto the receiver, namely heliostats, and their distribution on the ﬁeld.
Heliostats are comprised of a supporting structure, a mirror surface and a tracking system, Figure 2. The
tracking system enables the relative movement whereby the mirrors follow the sun and ensures that the reﬂected
beam aims at the receiver correctly. The aiming point is deﬁned by a central system and each heliostat has an
internal computer to calculate the correct, instantaneous relative positioning based on the position of the sun
and the aiming point. For tracking purposes, the heliostats have two degrees of freedom which, in practice, are
implemented as rotation around two axis. These axes might or might not be perpendicular. The most common
conﬁguration is the azimuth-elevation tracking system but there are other proposals like the target-aligned 
or the slope-drive  tracking . Nowadays, tracking algorithms are not able to compensate dynamically for
the sunspot position during operation. Also, the algorithms assume a rigid supporting frame not aﬀected by
external inﬂuences such as wind or weight deformation, and need to be calibrated periodically to correct any
miss-tracking. Several self-calibration systems have been proposed, but there is not a commercial solution yet.
Figure 2: Abengoa heliostat with 8x4 facets.
The mirrors are the critical part of the heliostats. They are responsible for reﬂecting the sun rays onto the
receiver. The highly reﬂective surface is typically a silver layer encapsulated between two protective layers. The
upper layer is a glass or glass-like surface that protects the reﬂective layer from harmful environmental agents
such as moisture, corrosion or abrasion. The back surface is normally a copper layer with protective paint.
This surface is glued to the supporting structure by diﬀerent techniques. For the glass surface, low weight
Review of Solar Subsystems 11Review of Solar Subsystems 11Review of Solar Subsystems 11
requirements are desirable but not critical, given that the main contributor to the mechanical design of the
frame is wind loads and not weight. The critical property for the glass surface is optical performance, such as
high transmittance (low iron composition), long lifetime with reduced O&M costs, easy cleaning and, in some
cases, high ﬂexibility. Aluminium and various metals are other possibilities for the reﬂective layer but they are
less common in commercial applications.
State-of-the-art heliostats can achieve aperture areas of more than 100 m2, such as Abengoa ASUP 140 m2
or Sener HE54 178.5 m2. The reﬂective surface is composed of an array of smaller mirrors called facets, as
seen in Figure 2. To reduce the size of the reﬂected spot on the receiver surface, these facets are not contained
on the same plane. On the contrary, the supporting frame provides an inclination to each individual facet so
that all of them aim to the same point. This inclination is called canting and its eﬀects can be seen in Figure 3.
Sometimes, the facet is also curved to achieve a further reduction of the size of the solar spot on the receiver.
Canting and curvature of facets can be used independently.
Figure 3: Eﬀect of canting on the receiver .
The supporting structure keeps the mirrors in position and avoids deformations that could compromise the
precision of the heliostat, which is tightly linked to the rigidity of the supporting structure. In order to ap-
prehend how important this is, it is worth noting that the distance from the heliostat to the tower can be as
long as 1 km, hence turning small variations of the heliostat geometry into several meters of aiming error at the
receiver. The supporting structure has an important share of the total cost of the heliostat, and diﬀerent designs
have been proposed to reduce the associated weight (hence costs) and, if possible, reduce deformations. The
foundations of the structure are usually made of concrete, specially for the larger heliostats. Smaller heliostats
12 Review of Solar Subsystems12 Review of Solar Subsystems12 Review of Solar Subsystems
make use of pedestals (poles) drilled into the ground directly, ground anchors or gravity-supported structures
. The type of foundation is selected based on the type and size of the heliostat to be installed, since a large
number of small heliostats (with less costly foundations and shorter installation times) could make concrete
foundations or even drilled-pedestals prohibitive. On the other hand, increasing the size of the heliostat is
actually an opportunity to reduce costs due to the reduced number of actions in spite of the deeper installation
of each foundation. The opposite happens for the drives. The smaller heliostats can use simpler and cheaper
drives, while the larger ones need more robust and expensive drives to move the supporting frame and mirrors
whilst avoiding unwanted movements as a consequence of wind or gravity loads.
In line with the foregoing discussion, heliostats of diﬀerent size have been proposed, with a general trend
towards larger sizes to reduce individual costs such as wiring, control boxes and other components. This scale-up
of the heliostats increases the requirements of the supporting frame and reduces its accuracy. Therefore, an
medium-size heliostat has recently been proposed as a compromise solution; nevertheless, there are no oper-
ational and economic data available yet to assess the economic gains relative to the +100 m2state-of-the-art
There are ﬁve eﬀects inﬂuencing the eﬃciency of a solar ﬁeld layout: cosine ηcos, atmospheric attenuation
ηaa, spillage ηsp (also called intercept factor), shadowing (both by the tower ηst and by neighbouring heliostats
ηsh) and blocking ηbl. These parameters vary for each heliostat and time instant, and the are normally evaluated
for a certain time of the year. Globaly, the eﬃciency of a particular layout is determined by a combination of
the previous eﬀects.
The diﬀerent patterns used to distribute the heliostats on the ﬁeld aim to maximize global eﬃciency, focusing
on a reduced number of parameters or on a combination of them, due to the complexity of analyzing the whole
problem. A lot of research has been devoted to this topic, and discussions are still ongoing. No optimal ﬁeld or
pattern has been found, and each project develops its own layout speciﬁcally for the site.
η=ηcos ηaa ηsp ηst ηsh ηbl (1)
Due to the ﬁxed position of the receiver on the tower, solar beams does not strike normal to the surface
of the mirrors. Therefore, the eﬀective area of the heliostat is smaller than the geometrical (aperture) area.
the associated cosine losses are deﬁned by the angle between the solar beam and the normal to the heliostat
surface deﬁnes , Figure 4, which means that the cosine factor depends on the position of the heliostat relative
to the tower, this eﬀect being stronger for heliostats in the south ﬁeld (considering that the plant is located in
the Northern hemisphere). The cosine eﬀect is purely geometrical and its impact is speciﬁc to each sun position.
The characteristic lengths involved in a typical solar tower ﬁeld are very long and hence it is mandatory to
account for the scattering of solar radiation across the air between heliostat and receiver. In general, atmospheric
attenuation is caused by three main compounds: gases, aerosols and clouds. Gases have approximately constant
concentration except for water vapour, whilst the concentration of clouds and aerosols ﬂuctuates in space and
time. This eﬀect is usually modelled with the Lambert-Beer-Bouquet transmittance model which depends on
local visibility through the extinction coeﬃcient (Equation 2):
Spillage represents the amount of reﬂected solar beams that miss the receiver surface. There are several
reasons for this, such as a bad aiming strategy, tracking errors, undesirable movement of the heliostats due to
wind loads or overﬂow of the sunspot on the receiver surface. This last eﬀect occurs when the heliostat is far
enough from the receiver and the reﬂected image size is larger than the receiver surface.
Review of Solar Subsystems 13Review of Solar Subsystems 13Review of Solar Subsystems 13
Figure 4: Cosine eﬀect .
When the sun is low in the sky (morning and evening), some of the heliostats project their shadow on a
neighbouring heliostat which, as a result, is partially covered as shown in Figure 5. At the same time, the
shadow of the tower over the solar ﬁeld covers a number of heliostats, an important eﬀect that is sometimes
ignored in order to simplify the optimisation problem. Blocking is similar to shadowing but, in this case, the
interception of beams takes place after these have been reﬂected, as shown in Figure 5 also.
Figure 5: Combined eﬀect of blocking, shadowing and cosine 
All these parameters depend largely on the height of the tower and the size of the receiver through the relative
position of each heliostat, adding complexity to the heliostat-distribution problem. It is due to the complexity
of this problem that diﬀerent patterns are proposed for the positioning of heliostat positioning, the most studied
of which are cornﬁeld, radial stagger and spiral [20, 21, 14, 22]. Some authors propose the combination of these
patterns to increase the eﬃciency of the solar ﬁeld [23, 24] whilst other propose a free-pattern system to max-
imise the global eﬃciency [25, 26, 27, 28] . This pattern-free system is very promising, but the computational
requirements are too high to be considered aside the academic ﬁeld. A diﬀerent approach to this problem is
performed by Carrizosa et al. , where the utilisation of heliostats of diﬀerent size in the same ﬁeld is proposed.
14 Review of Solar Subsystems14 Review of Solar Subsystems14 Review of Solar Subsystems
Figure 6: Heliostat distribution patterns.
At the moment, there are important limitations regarding materials of the receiver and stability of the HTF
at high temperature. These constraints limit the amount of heat ﬂux that can be delivered onto the receiver. It
is then mandatory to develop an aiming strategy that yields an homogeneous ﬂux over the receiver, avoiding hot
or cold spots. Aside from the loss of eﬃciency, those spots can be dangerous for the equipment inasmuch as hot
spots can trigger the degradation of the salts and receiver materials while colds spots can lead to solidiﬁcation
of the molten salts. The aiming strategy has been studied by diﬀerent authors [30, 31, 32, 33], and is a well
kept secret for each solar company. One of the main diﬃculties on this ﬁeld is to get knowledge of the real
aiming point of each heliostat. There is no reliable way of determining the exact pointing of each heliostat, nor
the exact amount of ﬂux over the surface of the receiver.
A solar receiver is nothing but a heat exchanger. It absorbs the concentrated solar ﬂux coming from the ﬁeld
of heliostats and transfers it to a working ﬂuid (molten salt or water/steam) in the form of either temperature
rise, phase change or both. Several classiﬁcations are possible according to criteria such as:
•Heat transfer ﬂuid: air, CO2, particle suspensions, water/steam, molten salts, thermal oil, liquid metals,
solid particles, helium, hydrogen .
•Geometry and/or arrangement of the absorption plane (surface impinged by the concentrated solar ﬂux):
external or cavity receivers.
•Internal layout of the heat exchanger: tubular, volumetric, suspension of particles, falling ﬁlm receivers.
The evolution of commercial solar tower plants for electricity generation can be tracked through the geom-
etry of the absorption plane. The ﬁrst generation used cavity receivers in order to reduce losses while external
receivers gained relevance later, in order to increase the aperture area of the receiver and, with it, the power
output. In cavity receivers, concentrated sunlight enters the receiver across the aperture plane (window) and is
trapped inside, hence bringing about fewer heat losses than an external receiver where the absorber is exposed to
intense heat exchange with the environment. This apparently high absorption capacity makes cavity receivers
especially favourable when a high operating temperature is sought, for instance when pursuing higher solar
shares (i.e. the fraction of heat input to the cycle coming from concentrated solar energy in hybrid CSP-STE
plants) . Cavity receivers may also incorporate a secondary concentrator mounted in front of the aperture
In external arrangements, the incident solar irradiation strikes the outer surface of the receiver. Losses
due to heat exchange with the environment are higher, but this conﬁguration allows a larger solar ﬁeld which
increases the maximum power output and reduces the strict requirements on aiming strategies and tracking
errors. Diﬀerent conﬁgurations are known for this technology, such as the cylindrical plane or crescent receiver,
Review of Solar Subsystems 15Review of Solar Subsystems 15Review of Solar Subsystems 15
the truncated receiver, billboard receiver or ﬂat-plate tubular panel .
The heat transfer ﬂuid in contemporary solar towers is molten salts or water/steam, thus state-of-the-art
receivers are based on these ﬂuids. Nevertheless, other options to increase the eﬃciency of CSP technology
using gaseous, liquid or solid HTFs are under development.
3.2.1 Gas Receiver
Gas receivers can be divided into (i) volumetric, (ii) tubular and (iii) particle suspension types depending on the
conﬁguration. It is nevertheless noted that even though suspension receivers are also included in this section,
they should lie in a diﬀerent category. Volumetric receivers (i) may be classiﬁed into atmospheric and pres-
surised systems, none of which enable enable storage, making it necessary to include an intermediate medium
for that purpose. This type of receiver is usually integrated into an open loop conﬁguration in combination
with a steam Rankine cycle. A blower forces a stream of air through the absorber material and, in turn, air
achieves a higher temperature. A waste heat recovery boiler downstream of the receiver takes advantage of the
energy carried by the air ﬂow to generate steam and eventually drive a turbine. It is interesting to note that the
PS10 power plant in Spain, which is currently using a cavity receiver for direct steam generation, was originally
conceived as an atmospheric air receiver .
Pressurised receivers have mostly been considered for gas turbine applications where they are installed down-
stream of the compressor to increase the temperature of compressed air. A closed loop conﬁguration consists
of a volumetric receiver receiving pressurised air at low or moderate temperature (this depends on the pressure
ratio of the engine) and delivering it at a higher temperature either to a supplementary combustor in series or
to the turbine directly. It is easily deduced that the lower the temperature gap between receiver outlet and
turbine inlet, the higher the solar share and hence the lower the carbon footprint of the electricity produced.
Pressurised air receivers are widely regarded as an alternative to fossil fuels, addressing issues such as increased
eﬃciency, reduced water consumption and higher ﬂexibility and dispatchability through hybridisation . High
pressure operation makes it necessary to install transparent windows to eﬀectively separate the receiver cavity
from the environment. The reliable operation of this window turns out to be critical to achieve the aforecited
goals both in terms of performance and reliability.
Tubular air receivers (ii) can conceptually be integrated into open loop or closed loop conﬁgurations de-
pending on the design pressure of the air ﬂow although, historically, the integration into a Brayton Cycle is
the usual approach. The SOLUGAS plant was the ﬁrst megawatt scale hybrid gas turbine system operating on
concentrated solar energy and natural gas simultaneously . It was designed, constructed and operated by
Abengoa Solar at the Sol´ucar Platform in Seville, Spain. The receiver was a tubular cylinder comprised of 6
metre long pipes with a total diameter of 5 metres. Neither secondary concentrator nor glass window were con-
sidered. The design speciﬁcations were an outlet temperature of 800oC and 80% eﬃciency. The demonstration
phase was successful and conﬁrmed the operability/feasibility of the system .
A dense suspension of particles (DPS) is a combination of the classical solid particle heat transfer medium
and an air/gas stream (iii). It takes advantage of the high temperature properties of solid particles and the easy
handling of gases. The DPS consists of very small particles which can be ﬂuidised at low gas speeds, thus being
easily transported similarly to a gas. The operating principle of a DPS receiver relies on creating the upward
circulation of a DPS (solid fraction in the range 30-40%) in vertical absorbing tubes subjected to concentrated
solar energy irradiation. The higher the particle velocity, the higher the heat transfer coeﬃcient, due to the
increase in particle agitation. In addition, the higher the particle volume fraction, the higher the heat transfer
coeﬃcient, since particles occupy a larger volume and hence the contact area with the tube walls is larger as
well . The main advantages of this technology are the capability to reach high temperatures of up to 1000oC
 and the possibility to be used directly as a storage solution. Also, from the point of view of reliability and
safety, the lack of freezing issues and risk of explosion are very positive features of particles.
16 Review of Solar Subsystems16 Review of Solar Subsystems16 Review of Solar Subsystems
3.2.2 Liquid Receiver
There are diﬀerent conﬁgurations of liquid receivers under study, but the only promising and already commercial
type are the tubular receivers. Tubular receivers have been developed and used in various projects since the
1980’s (demonstration plants Solar One , Solar Two , RAS  and CESA-1  are some remarkable
examples). Fluids typically used have been water/steam and molten salts. Alternative ﬂuids mentioned in
literature but not implemented commercially are carbonates, chlorides and metals . Using water as a basic
ﬂuid has important environmental advantages but there are also several shortcomings. Amongst the former,
it is worth noting the almost null environmental impact of any water/steam leakage and the direct use of this
ﬂuid as working ﬂuid in the Rankine power block. Amongst the disadvantages, the maximum heat ﬂux that the
receiver is able to withstand, in the range from 200-500 kW/m2, and the lower thermal capacity when compared
to molten salts or sodium. The ﬁrst commercial projects implementing these receivers used saturated steam at
intermediate pressure and temperature (PS10 and PS20), due to design (all the receiver as evaporator), safety
(lower risk of hot spots due to absence of superheater) and operability (just wet steam production) concerns.
Later commercial projects though, like Khi Solar One or Ivanpah, used superheated steam as working ﬂuid with
temperatures over 500oC . Even if a superheated steam receiver increases the complexity in terms of design
and operation, it enables higher eﬃciencies in the Rankine cycle.
Molten salt receivers (typically a mixture of NaNO3and KNO3) are, on the other hand, getting more and
more usual in the commercial projects that are currently under development and construction. The main reason
for this popularity is the implementation of thermal energy storage systems, which are currently considered a
mandatory feature of this technology (for dispatchability considerations). Indeed, in tubular receivers using
molten salts, a fraction of these are sent to the steam generator (heat exchanger) whilst the remaining ﬂow is
sent to a hot insulated tank for storage. Another clear advantage of using molten salts is the higher heat ﬂux
admissible on the solar receiver surface (due to a higher heat capacity of the ﬂuid ﬂowing on the inside), which
enables higher concentration factors than for steam technology, hence higher eﬃciencies. Accordingly, the utili-
sation of molten salts brings about a generalised increase in performance both at component and system levels.
Amongst the shortcomings, the decomposition of salts limits the operational temperature to less than 600oC
, a very large inventory of salts is needed (in particular when large storage capacities are incorporated),
and the freezing point increases to over 220oC, which requests auxiliary equipment to prevent solidiﬁcation.
Nonetheless, in spite of these operational and constructive diﬃculties, the number of molten salts based power
plants in the pipeline is not declining. A more detailed explanation below can be found in Section 3.3.
3.2.3 Solid Particle Receiver
The concept of falling solid particles receiver consists of sand-like ceramic particles falling across a directly
illuminated cavity receiver whilst absorbing heat by radiation. This concept enables easier implementation of
storage capability and scale-up of the technology, hence exploiting the thermal properties of solid particles.
Ceramic materials such as alumina, silica and zircon are good candidates, and other materials like iron-doped
Al2O3 spheroid have also been proposed for the particles . Receivers with windows and aerowindows have
been considered with expected eﬃciencies in the range of 80%, even if the prototypes have not exceed 50% .
In this regard, there are some parameters of inﬂuence that have to been taken into consideration in the design
phase, such as type of particle [51, 52] and the aerowindow air jet ﬂow [53, 54]. Other innovative solutions
like the use of magnetic ﬁelds to increase the residence time and thermal absorptance of particles, as well as to
reduce the particle ﬂow destabilisation, have been assessed with computational models . From an experi-
mental standpoint, a centrifugal particle prototype has been designed by DLR with a thermal power of 500 kW
and target particle temperature of 900oC; this prototype is expected to be tested in the near term at the J¨ulich
tower facility . On the negative side, technical solutions for other aspects like heat exchanger design and
particle conveyance technologies are noted as important concerns for this technology. In this regard, remarkable
Review of Solar Subsystems 17Review of Solar Subsystems 17Review of Solar Subsystems 17
Figure 7: Liquid, external tubular receiver developed by Torresol c
research is going on at Sandia National Labs, where various solutions are being developed and tested, with the
aim to demonstrate a complete unit at the small scale [57, 58]. Finally, regarding the practical implementation
of solid particles receivers into the power plant, this category of receivers can be integrated into the power cycle
through a ﬂuidised bed heat exchanger. Steam or gases are possible heat transfer ﬂuids, depending on heat
exchanger design, thus both Rankine and Brayton cycles are feasible power block technologies.
3.3 Thermal Energy Storage System
Thermal energy storage solves the mismatch between solar energy supply and electricity demand, providing
a distinctive advantage of STE plants over other renewable technologies like wind or photovoltaic . To
date, electrical energy storage using batteries at the large scale is not technically or economically feasible
[59, 60, 61, 62, 63, 64] in comparison with other energy storage technologies like Thermal Energy Storage. No
problems of shortage of storage media like water or nitrate mixtures are foreseen in the future, contrary to the
uncertainty regarding lithium batteries, where large a much larger demand is foreseen within the next years .
Solar power plants with thermal energy storage systems can have diﬀerent operational strategies, depending
on the daily variations of supply/demand proﬁles. TES systems can be integrated to perform the following
functions [66, 67]:
•Mitigation of short ﬂuctuations during transient weather conditions, e.g. cloudy periods. Those periods of
inclement weather can force the turbine to be operated in transient conditions, thus reducing the turbine
eﬃciency due to start-up losses. Even if heat transfer ﬂuids have some thermal inertia that could help the
plant continue operating during short cloudy periods , the experience with large-scale facilities shows
that it may not be enough to prevent turbine shut-down . Small capacity storage systems could help
to mitigate these short ﬂuctuations of solar radiation.
•Shifting the generation period from peak hours of solar insolation to peak hours of power demand. Thermal
energy storage systems can improve dispatchability by storing energy during oﬀ-peak hours and then
discharging it during hourse of peak demand .
•Extending operation beyond sunset, hence acting as baseload electricity generation and improving the
annual capacity factor (this requires much larger solar ﬁelds than in plants without storage). This annual
capacity factor is deﬁned as a performance parameter that compares the net electricity delivered by the
solar facility to the energy that could have been produced should the plant have been operated at full
capacity throughout the year. Given that the solar resource is only available during some hours of the
18 Review of Solar Subsystems18 Review of Solar Subsystems18 Review of Solar Subsystems
day, thermal energy storage systems can improve the capacity factor enabling power generation when the
sun is not available.
Two diﬀerent thermal energy storage technologies are currently implemented in commercial solar thermal
electricity plants: (i) steam accumulation in direct steam generation plants, and (ii) two-tank molten salt sys-
tems in either parabolic trough with thermal oil or solar tower with molten salt indirect steam generation plants.
3.3.1 Storage based on steam accumulation
Water can be used as heat transfer ﬂuid and storage medium in so-called Direct Steam Generation (DSG)
plants. DSG is commercially available today and it eliminates the need for intermediate heat transfer ﬂuids
while increasing overall plant eﬃciency and reducing the environmental impact. The steam produced in the
receiver is supplied directly to the turbine without any intermediate heat exchanger. In addition, the limitations
on peak operating cycle (live steam) temperature set by the degradation of the thermal oil (above 400oC) or
nitrate molten salts (above 565oC) are released which enables more eﬃcient power cycles . Furthermore,
investment costs are reduced due to the elimination of intermediate equipment.
Actually, steam accumulators are the only commercial TES solution for DSG plants. A steam accumula-
tor is an active direct storage system based on the Ruth accumulator system, where steam is stored at high
pressure in accumulator tanks directly. As of September 2019, there are only three commercial tower plants
in operation using steam accumulators to store thermal energy: PS10, PS20 and Khi Solar One, all of them
developed by Abengoa. PS10 and PS20 started commercial operation in 2007 and 2009, respectively, and they
became not only the ﬁrst two commercial solar towers in the world but also the starting point for the operation of
direct steam generation technology. These ﬁrst generation CSP towers use saturated steam as shown in Figure 8.
Figure 8: Schematic ﬂow diagram of a direct steam generation tower plant with thermal energy storage system
based on steam accumulation.
The second generation of CSP-DSG plants make use of superheated steam (Khi Solar One, 2016). In these
superheated steam solar towers, a second receiver with the main function to re-heat the steam produced by the
ﬁrst receiver (evaporator) is needed, enabling higher temperatures than in ﬁrst generation plants. Live steam,
which feeds the turbine, can thus reach temperatures and pressures in excess of 540oC and 130 bar, thereby
enhancing the eﬃciency of the power cycle by 30% relative to its forerunner PS20. Khi Solar One, a 50 MWe
superheated steam tower, has a storage capacity of around 2 hours thanks to nineteen steam accumulation tanks
which store saturated steam produced in the evaporators. This steam feeds the turbine when needed, enabling
Review of Solar Subsystems 19Review of Solar Subsystems 19Review of Solar Subsystems 19
power generation even when there is no sun. This is shown in Figures 9 and 10.
Figure 9: Schematic ﬂow diagram of a direct superheated steam generation tower plant with thermal energy
storage based on steam accumulation.
Figure 10: Steam accumulators in Khi Solar One.
Steam accumulators use sensible heat storage in the form of pressurised saturated liquid water , where
the liquid and gaseous phases are in thermodynamic equilibrium. They proﬁt from the high volumetric storage
capacity of liquid water for sensible heat due to its high speciﬁc heat capacity . Water is used as both
storage medium and working ﬂuid, so high discharge rates are possible, while the storage capacity is limited
by the volume of the pressure vessel. The speciﬁc energy sorage capacity depends strongly on the variation of
saturation temperature resulting from the pressure drop during the discharge phase, with characteristic values
in the range of 20-30 kWh/m3.
A steam accumulator is a steel pressure tank designed to withstand high pressure and temperature wa-
ter/steam. Figure 11 shows a schematic representation of a steam accumulator, including its internal compo-
nents. Steam accumulators usually have cylindrical bodies and elliptical bonnets, as this is the most eﬀective
shape from a mechanical standpoint, abd they are made of carbon steel. For the design of such equipment, it is
important to take thermal cycling into account to ensure that the material is able to withstand the continuous
operation under variable conditions. To avoid problems related to thermo-mechanical stress in the accumulators,
20 Review of Solar Subsystems20 Review of Solar Subsystems20 Review of Solar Subsystems
temperature gradients in the vessel walls must be limited. Furthermore, even if the materials commonly used in
these equipment are well-know, corrosion phenomena due to water impurities should not be overlooked. Finally,
there are limitations regarding the maximum size of each steam accumulator, mostly due to peak pressure and
to transportation concerns. However, several units can work in parallel to meet the total thermal energy storage
requirements of the plant.
Figure 11: Variable-pressure steam accumulator .
During operation, steam accumulators are partially ﬁlled with water, commonly ranging from 50% to 90%
of the total volume. The accumulator system is charged with the surplus saturated steam produced in the
evaporator receiver (not used to produce superheated steam for the turbine). This surplus steam is injected
into the pressurised storage vessel by means of a distribution manifold, which is ﬁtted with steam injectors
or nozzles. The nozzles are a crucial component in a steam accumulator due to their variable performance
(injection rate) as the pressure in the vessel increases. The steam injected by the nozzles forms bubbles that
increase the pressure of water/steam, leading to a higher saturation temperature. When correctly designed and
operated, steam from a steam accumulator is clean, with steam quality approaching unity. During the discharge
phase, steam is produced by lowering the pressure of the saturated liquid. When the pressure inside the tank
drops, ﬂashed steam is generated at the rate demanded by the power block and the water level inside the tank
If superheated steam is desired, a separated higher-pressure steam accumulator is needed along with a
steam/steam heat exchanger to reach superheated conditions. The ﬁnal result is an increase in cycle eﬃciency
and, therefore, the global eﬃciency. Khi Solar One uses this two pressure level steam TES conﬁguration eﬀec-
3.3.2 Storage based on molten salts
Molten salt is the most widespread storage material in commercial CSP applications due to its good thermal
properties and reasonable cost. Nowadays, molten salts provide a thermal storage solution for the two most
mature technologies available in the market (i.e., parabolic trough and solar tower) and they can be used in
either direct or indirect storage conﬁguration, depending on the solar ﬁeld technology of the plant under con-
sideration. In either case, trough and tower technologies, the conﬁguration of the storage system is based on
two tanks, at high and low temperature. This concept was successfully demonstrated in diﬀerent solar thermal
demo plants : CESA-1 (Spain) [74, 75], Themis (France) [76, 77], CRTF (USA) , Archimede (Italy)
[79, 80] and Abengoas 8.1 MWhthstorage capacity TES-MS (Spain) [81, 82, 83]. The 10 MWe Solar Two
demonstration tower plant in USA also demonstrated a 105 MWhth storage capacity TES system successfully
[69, 84, 85], and it is actually considered the ﬁrst pre-commercial scale two-tank molten salt storage system.
Review of Solar Subsystems 21Review of Solar Subsystems 21Review of Solar Subsystems 21
Solar Two operated from 1996 to 1999 and helped validate nitrate salt technology and reduce the technical and
economic risks of molten salt technology .
Commonly used molten salts are based on nitrate mixtures with a weight composition of 60% NaNO3and
40% KNO3and an operating temperature range between 290oC (freezing point is 240oC) and 565oC (limited by
thermal degradation). This ﬂuid is usually called Solar Salt and, nowadays, it yields optimum cost and thermal
properties for the CSP industry. These sodium and potassium nitrate mixture has been very well known by
the solar industry for decades, with wide bibliographic information and proven feasibility at both pilot and
commercial scales [86, 87, 69, 73, 74, 75, 76, 78, 79, 80, 81, 82, 83, 84, 85].However, corrosion phenomena is
still an ongoing topic for research, and material compatibility due to impurities in these mixtures is yet to be
optimised. Nevertheless, satisfactory performance with the most common materials used in the solar industry
can be assured [73, 88, 89, 90, 91, 92, 93].
Due to the strong demand for molten salts by the CSP industry, an active search for suitable molten salts
mixtures to be used as heat transfer ﬂuid and storage material has been going on in the last years [6, 94, 95]. In
addition to the Solar Salt, the most relevant molten salt candidates to be used in solar thermal power plants are
Hitec salt, a ternary mixture of NaNO2, NaNO3, and KNO3, and Hitec XL R
, a ternary mixture of Ca(NO3)2,
NaNO3, and KNO3. These two ternary mixtures have been considered as potential replacement for the
standard Solar Salt due to theor low freezing point, 142oC and 120oC respectively . However, their max-
imum operating temperature is also signiﬁcantly lower than that of the Solar Salt. Hitec is thermally stable
at temperatures up to 454oC and it may be used at temperatures up to 538oC but for a short period of time
only . Hitec XL, a mixture of 48%(wt) Ca(NO3)2, 7%(wt) NaNO3and 45%(wt) KNO3may be used at
temperature up to 500oC [10, 98, 99, 100, 101, 102, 103].
In general, molten salts are an interesting storage material due to its high energy storage capacity (per spe-
ciﬁc volume) and very high thermal inertia (high heat capacity and low thermal conductivity). These thermal
properties allow designing storage systems with minimum thermal losses, increasing the global eﬃciency of the
plant. Nevertheless, using molten salts to store thermal energy has inherent risks due to their high freezing
point. Electric heat tracing systems and tank heaters are installed to minimise the risk of a freezing event and to
avoid critical thermal gradients during start-up. However, these equipment involve high parasitic consumption
to maintain the salts in molten state even when the system is completely discharged.
3.3.3 Steam Generator
In solar towers using molten salt technology, there are one or more trains of heat exchangers to transfer the
energy from the molten salts to the working ﬂuid of the cycle. This working ﬂuid is usually water, which is
evaporated and superheated. This process is carried out in two or more heat exchangers. Standard conﬁgurations
include an economiser to preheat water, a boiler for evaporation, a superheater to increae the temperature of
saturated steam and a reheater to increase the temperature of steam that has been partially expanded in the
high-pressure section of the turbine. All these heat exchangers are usually of the shell and tube type, with the
molten salts ﬂowing on the shell and steam ﬂowing inside the tubes, also for the evaporator. This conﬁguration
is nevertheless not standard in the industrial shell and tube boilers, where steam is on the shell side. In molten
salt steam generators, molten salts are always on the shell side to simplify the electric heat tracing and to avoid
possible salt freezing. This decision is not unanimous in the industry, with diﬀerent suppliers preferring to
have water boiling on the shell side in a standard kettle conﬁguration as typically used in waste heat recovery
applications. The tubes are also heat traced but, in this case, with steam coming from an auxiliary boiler. To
facilitate free draining and natural circulation, all heat exchanger and piping are installed staggered and with
a minimum slope of 10%. The pressure drop across the exchangers is minimised to reduce auxiliary electric
22 Review of Power Block22 Review of Power Block22 Review of Power Block
4 Review of Power Block
4.1 Fundamentals of Rankine Cycles for Steam Turbines
Power cycles convert energy in the form of heat Qin received from a source at high temperature THinto shaft
work Wshaft . The fraction of energy put into the cycle that is not converted into work is rejected as heat Qout
to a low temperature sink at TL. This is shown in Figure 12.
Figure 12: Elementary power cycle.
The restrictions set forth by the First and Second Laws of Thermodynamics imply that the amount of heat
rejected to the low-temperature sink be not null (Qout >0), and that the total amount of energy and entropy
being exchanged be balanced1 2:
Qin =Qout +Wshaft (3)
Where δS stands for the production of entropy within the system (cycle). From Eqs.(3,4), the following
mathematical expression to calculate 1st Law eﬃciency can be obtained:
Given that, according to the 2nd Law, ∆S≥0, it follows that the highest eﬃciency is achieved by a reversible
engine for which ∆S= 0:
ηCarnot = 1 −TL
In an actual power plant (or engine), heat addition and heat rejection do not take place at constant temper-
ature nor are the energy exchange and conversion processes reversible. Therefore, this eﬃciency ηC arnot sets a
higher limit of eﬃciency which cannot, in practice, be achieved. Nevertheless, the following guidelines for the
thermodynamic assessment of power cycles can be drawn:
1Not that these conservation equations apply to non-reacting systems where heat and mechanical work only are involved.
2In the remainder of this section, it is assumed that heat is added to and rejected by the cycle at constant temperature.
Review of Power Block 23Review of Power Block 23Review of Power Block 23
•Heat addition at the highest possible temperature and heat rejection at the minimum temperature possible
favour high cycle eﬃciencies.
•Most of the times, heat addition and rejection do not take place at constant temperature, what increases
the irreversibility of these processes. In these cases, the concept of mean thermodynamic temperature of
the process might be useful:
With this new tool, the foregoing statement can be reworded as follows: heat addition at the highest
possible mean temperature and heat rejection at the minimum mean temperature possible
favour high cycle eﬃciencies.
•Reducing the irreversibility of the thermo-mechanical energy conversion devices like pumps, compressors
and turbines favour high cycle eﬃciencies.
This simple analysis suﬃces to assess the interest and limitations of the power cycles commonly used in
Concentrated Power Plants and also to evaluate the potential of other cycles like those based on supercritical
The Carnot cycle is the only cycle able to achieve the eﬃciency quoted in Eq.(6), as long as both heat transfer
between the cycle and the source/sink and thermo-mechanical energy exchange are carried out reversibly. Such
cycle is presented in Figure 13 and, even if very eﬃcient, it suﬀers from very low speciﬁc work (i.e., power output
per unit mass ﬂow rate of working ﬂuid) inasmuch as most of the work produced by the expander is consumed
by the compression process. Additionally, it also happens that the temperature diﬀerence between the source
and the hot working ﬂuid and between the cold working ﬂuid and the sink is a source of irreversibility, as so are
the compressors and turbines. As a result of this, not even a practical Carnot engine would be able to achieve
the eﬃciency quoted above.
Figure 13: Ideal Carnot cycle.
The Rankine cycle is another embodiment of a power cycle which aims to get as close to the Carnot cycle
as possible, thermodynamic-wise. It is characterised by a istohermal/isobaric heat rejection in the condenser,
close to ideally isentropic compression of the working ﬂuid in liquid state, isobaric heat addition at variable
temperature (except for the phase change part of heat addition) and isentropic expansion. This is shown
in Figure ?? for a cycle were compression and expansion are irreversible (non-ideal cycle) and heat addition
experiences a non-negligible pressure drop (ca. 20%). The main design parameters of the cycle are:
•Live steam temperature: live steam temperature should be as high as possible in order to enable higher
thermal eﬃciencies, as deduced from Eq.(6). This is limited by either steam turbine materials (this would
be the case of a coal power station or a steam turbine in a modern combined cycle power plant) or by
24 Review of Power Block24 Review of Power Block24 Review of Power Block
a the temperature of the heat source (this is the case of a Concentrated Solar Power plant where the
temperature of the Heat Transfer Fluid is limited by thermo-chemical stability).
•Live steam pressure: high live steam pressure are usually sought as these bring about higher thermal
eﬃciency. Nevertheless, very high turbine steam pressures have a negative eﬀect on cycle eﬃciency as a
consequence of a drastic reduction of speciﬁc output (kJ/kg). Therefore, for each live steam temperature,
an optimum value of live steam pressure can be found.
•Condenser pressure: reducing the saturation temperature in the condenser has a very strong positive
eﬀect on cycle eﬃciency, according to Eq.(6). Indeed, lower condenser pressures enable much larger
turbine expansion ratios which, even though requiring more complex turbine designs, boost speciﬁc output
Condenser pressure is therefore set to the minimum possible value enabled by ambient conditions and by
the cooling technology of choice (whether air or wet cooling). In practice, this translates into condenser
pressures ranging from 50 to 150 mbar (5 to 15 kPa).
The design space where the values of these parameters can be set is nevertheless bounded by mechanical
constraints. In addition to the pressure and temperature limitations, already cited, the most noteworthy lim-
iting factor is humidity. The condensation of steam along the expansion path brings about thermodynamic
(supersaturation) and aerodynamic losses which reduce the gross output delivered by the turbine. In practice,
increasing live steam pressure and reducing condenser pressure both bring about lower steam quality at turbine
exhaust, preventing the cycle from achieving the theoretical, peak thermal eﬃciency. In order to sort this prob-
lem out, it is customary to reheat the working ﬂuid halfway through the expansion process. Partially expanded
steam is hence heated up again at constant pressure and then expanded again in the turbine. This shifts the
expansion line rightwards in the Mollier diagram what has the eﬀect of leaving the exhaust steam closer to
saturated conditions. In practice, steam quality should not be lower than 0.8 if the life of blades in the last
stages is to be not compromised .
Reheat has thus the objective to increase steam quality in the low pressure section of the turbine and, with
this, increase the isentropic eﬃciency of this component. This has a positive impact on thermal eﬃciency of
the cycle. Additionally, when performed at the correct pressure, reheat brings about a thermodynamic beneﬁt
beyond that associated to the better aerodynamic performance. This optimum reheat pressure is between 20
to 25% of the pressure at turbine inlet (live steam) and enables some 4-5% higher thermal eﬃciency than in
non-reheated cycles .
The heat addition process is comprised of three diﬀerent steps. Water delivered by the pump is heated up to
the saturation temperature in the economizer, which is an open heat exchanger. Saturated water is evaporated
in the evaporator, usually a closed-circuit heat exchanger with either forced or natural circulation. Finally,
saturated steam is heated up to the target live steam temperature. Amongst these process, the economizer has
a very negative eﬀect on cycle eﬃciency due to its very low temperature and large enthalpy rise (note that con-
densate ﬂows into the economizer at around ambient temperature and ﬂows out at the saturation temperature
corresponding to live steam pressure, around 340oC). In order to raise the average temperature of (external)
heat addition to the cycle, it is customary to preheat the feedwater delivered by the pumps before entering
the steam generator. This is done from within the cycle, in a series of feedwater heaters whose heat source is
steam bled from the turbine. This steam from the turbine is bled at diﬀerent locations along the ﬂowpath, in
order to accommodate its the corresponding saturation temperature to the target feedwater temperature at the
outlet from the preheater. As a result of this, the duty of the economizer (and of the entire steam generator)
is reduced and the eﬃciency of the cycle increases, despite the lower expansion work .
Akin to the reheat process, the process of selecting the temperature rise across each feedwater heater, the
total number of heaters and the precise location (stage) at which steam is bled from the turbine allows for some
optimization. Extracting steam at higher pressure enables a lower mass ﬂow rate for the same heating capacity
but it also reduces the enthalpy change of the bled steam ﬂow. Overall, the following general rule of thumb
can be put forward, as a simpliﬁcation of the recommendation provided by Haywood : ”for maximum
Review of Power Block 25Review of Power Block 25Review of Power Block 25
eﬃciency in a non-reheat plant, the feedwater enthalpy rise should, to a ﬁrst approximation, be
the same in all heaters and in the economizer”. This rule applies to non-reheat plants and refers to
enthalpy change across each feedwater heater. Nevertheless, it provides a good starting point to be applied to
reheat cycles, also applied to temperature rise: ”for maximum eﬃciency in a reheat plant, the feed-
water tempreature rise should, to a ﬁrst approximation, be the same in all heaters and in the
economizer”. This is inaccurate inasmuch as the temperature rise across the feedwater receiving steam from
the ﬁrst extraction port downstream of the reheating process enables a larger temperature rise, and the contrary
applies to the last extraction port upstream of the reheater. Nevertheless, it is again stated that this simple
rules provides a good approximation from which further cycle reﬁnement can be carried out with simple tools
and little computational burden.
A ﬁnal comment regarding optimization of feedwater heating trains is mandatory when it comes to Concen-
trated Solar Power plants. Feedwater temperature at the outlet form the last heater before the steam generator
is linked to the outlet temperature of the Heat Transfer Fluid serving as heat carrier, be it molten salts or
synthetic oil. Therefore, feedwater temperaure might be constrained by the minimum temperature of the heat
transfer ﬂuid. For molten salts, this is related to freezing of the salts. For synthetic oils, this comes determined
by the higher viscosity at low temperatures which can potentially increase pumping power in the solar ﬁeld
signiﬁcantly. In either case, the ﬁnal temperature of feedwater in a Concentrated Solar Power plant might be
driven by these operational constraints rather than by the thermodynamic optimum.
The layout of a state-of-the-art Concentrated Solar Power plant using tower technology and steam turbines
is shown in Figure 14. The following elements are worth noting:
•Live steam temperature is limited by the temperature of molten salts at the outlet from the solar receiver
(and hot tank).
•Live steam pressure is at the optimum value balancing speciﬁc output and thermal eﬃciency.
•Reheat is performed at about at one fourth the pressure at the inlet to the high-pressure section of the
•Reheat temperature is again limited by the temperature of molten salts.
•Steam quality at the outlet from the low-pressure turbine is slightly below 20%, close to the allowable
limits of conventional steam turbines.
•A very large number of feedwater heaters are supplied with steam bled from the turbine at diﬀerent
extraction ports. All these heat exchangers work with similar terminal temperature diﬀerence.
•The temperature of feedwater at the inlet to the steam generator is such that the molten salt stream
returning to the cold tank is above the freezing point (220-240oC). This constraint is of a stronger priority
than the optimum temperature rise distribution from a thermodynamic standpoint.
4.2 Power Block in a CSP-STE power plant
To extract the thermal energy of the HTF and transform it into mechanical work, most CSP plants use a Rank-
ing cycle. In this cycle, the power block is responsible for generating electricity from the thermal energy carried
by the working ﬂuid (water/steam on state of the art CSP plants). The high temperature and high-pressure
steam obtained in the steam generator passes through a machine called turbine, where this steam moves a shaft
that, in turn, moves a synchronous generator, transforming the thermal energy into mechanical energy and then
into electricity that is eventually exported to the grid. A more detailed explanation of the water/steam power
block is provided later.
Commercial solar tower plants today make use of a steam Rankine cycle, operated on demineralised water.
Water at the outlet from the condenser is pumped towards the steam generator by low and high pressure pumps
and through a number of heat exchangers (feedwater heaters) fed by high pressure/temperature steam bled
from the turbine. The steam generator receiving thish high temperature subcooled water is then responsible
26 Review of Power Block26 Review of Power Block26 Review of Power Block
Figure 14: Heat balance of a state-of-the-art Concentrated Solar Power plant using tower technology.
for the production of superheated steam, for which aim it makes use of high temperature molten salts produced
by the tower (and stored in the high temperature storage tank). The superheated steam ﬂow coming out from
the steam generator is then directed to the turbine where it is expended to produce shaft power to drive the
electric generator. Once expanded to the lowest possible pressure (determined by ambient temperature and
condenser technology), the exhaust steam from the turbine is sent to the condenser where it reaches the liq-
uid state again. The associated latent heat is rejected to the environment by menas of either water or air cooling.
The main components of the power block are:
•Main cooling system and condensate tank. Most CSP plants today make use of Air Cooled Condensers. In
these, exhaust steam from the turbine ﬂows inside inclined, ﬁnned pipes on the outside of which ambient
air is forced by a number of fans. Older plants made use of water cooled condensers with forced draft
cooling towers but this is not used today in an attempt to reduce water consumption of the plant.
•Condensate (low-pressure) pumps are usually two stage pumps that operate with a high vacuum on the
•Feedhwater heating system. Between the condensate tank and the steam generator, a number of heat
exchangers are responsible for increasing the temperature of feedwater in order to increase the thermal
eﬃciency of the cycle. These shell and tube heat exchangers take steam from the turbine at high or low
pressure and transfer the associated sensible/latent heat to the feedwater ﬂow. Additionally, this turns
out beneﬁcial to ensure that the temperature of molten salts in the econmiser does not fall below the
freezing point. The number of feedwater heaters is in the range from 4 to 6.
•Deaerator. One of the feedwater heaters is nevertheless not of the shell and tube side. Indeed, halfway
from the condensate tank to the steam generator, an open heater is used with the same purpose as the
heaters mentioned in the foregoing bullet point. Additionally, this large storage tank is used as a reservoir
of hot water which can quickly react to a water demand by the steam generator if the plant is ramping-up
or operating in transient conditions.
The deaerator is located at the highest elevation of the power block and it is usually sized to enable at
least ﬁve minutes operation at full load. The water level inside the deaerator is kept at about 70% when
the plant operates in stationary conditions.
Finally, the deaerator is also responible for removing oxygen and other dissolved gases that may be present
in the working ﬂuid.
•Feedwater Pumps are usually multi-stage, volute type centrifugal pumps. These pumps, located at the
outlet from the deaerator, are responsible for increasing the pressure of feedwater as required by the steam
Review of Power Block 27Review of Power Block 27Review of Power Block 27
turbine. The powr consumption of these high-pressure pumps is hence not negligible.
•Solar steam generator. The heat transfer ﬂuid in an indirect steam generation plant transfers thermal
energy to produce high pressure steam. This steam Generator is comprised of four diﬀerent heat exchang-
ers: superheater, reheater, evaporator and preheater (or economiser). More information has already been
provided in an earlier section.
•Steam turbine. Steam turbines in CSP plants are usually arranged in two sections, high and intermediate-
low, with reheat in between them. They are usually assembled on the same shaft along with the electric
generator, all rotating at either 3000 or 3600 rpm. The usual gross output of these turbines is 50-100
MWe even though cost optimisation suggests increasing this to 150-200 MWe.
4.3 Auxiliary systems of the power block
In order to be able to compare the steam cycle with other alternative cycles like sCO2, it is important to note
that the power cycle requires auxiliary systems for operation during both start-up and shutdown manoeuvres
and also for normal operation (either at full or partial load). The most important auxiliary components are
•Turbine bypass lines (HP and LP): the HP bypass line must be able to manage up to 100% of the steam
generator outlet stream, reducing both pressure and temperature down to cold reheat conditions. The
LP bypass line performs the same action on the hot reheat steam ﬂowing out from the reheater, whose
pressure and temperature are reduced acceptable conditions to enter the condensate tank. In both cases,
high and low pressure, these bypass valves are required to act very rapidly.
•Intermittent/continuous blowdown: removal of dissolved and undissolved solids in water s mandatory in
order to control conductivity and other quality parameters of the working ﬂuid. The continuous blowdown
(or surface blowdown) is used to remove dirty water (with dissolved solids and impurities in suspension)
and replace this by fresh water. The intermittent blowdown has the main purpose of draining dirty water
from the bottom of the steam generator (with mud and sediment that accumulates in this area) and
replacing this with clean water.
•The lube oil system supplies oil for the turbine-generator assembly elements that are lubricated: bearings,
turbine overspeed bolts, turning gear bearings and mechanical drive, oil pumps and seal oil systems. This
lube oil circuit must also incorporate oil coolers in order to ensure accurate and reliable management of
lube oil temperature.
•An auxiliary boiler is often used to start up the power plant. Initially, the auxiliary boiler generates steam
in order to increase piping pressure and temperature (especially piping towards the HP and LP turbines).
Steam from the auxiliary boiler is also used to heat the deaerator.
•Gland sealing system. Gland steam is steam used to reduce the amount of steam leaking out of the
turbine through the gaps between rotating and stationary turbine parts (mostly casing and shaft but also
valve stems and others) and to prevent air from ﬂowing into the water/steam circuit at the low-pressure
end of the turbine (which remains below atmospheric pressure). Steam used in the gland seal system is
usually condensed in an independent, dedicated condenser rather than in the main condenser. This gland
steam condenser operates at a higher pressure than the main condenser and it is cooled by the condensate
ﬂowing from the condensate tank to the deaerator.
•Ejector or vacuum pump. These elements enable the low pressure that is needed in the condenser, also
ensuring that this turbine exhaust pressure is within the range recommended by the manufacturers of
turbine and condenser during start-up or transient operation but also in stationary operation if that is
•Demineralised water production is performed in the treatment plant where raw water is treated to comply
with the speciﬁc purity requirements deﬁned by the steam cycle. In normal operating conditions, water
consumption is mostly due to blowdown in the steam generator, venting from the deaerator and leakage
(structural leakage, valves not properly sealed, etc.). The amount of make-up water to compensate for
this water consumption in a steam cycle is lower than 2% of the rated mass ﬂow rate but this can change
depending on the operation of the cycle (for instance, it will expectedly increase in power plants with
28 Review of Power Block28 Review of Power Block28 Review of Power Block
continuous start-ups and shurdowns).
4.4 Design and performance of the steam cycle
As already discussed, the basic steam cycle is optimised with a certain number of extractions in the turbine, and
generally with a reheated steam (from cold reheat to hot reheat) in the steam turbine. The turbine expansion
process normally ends in the liquid-vapour zone, with the associated appearance of moisture in the last stages
of the turbomachinery. The appearance of wet steam causes aerodynamic and even mechanical problems that
compromise the performance and mechanical integrity of the turbine.
In order to increase steam quality at turbine exhaust, it is customary to reheat reheat the steam stream
halfway through the expansion, between the high pressure and low pressure steam turbine cylinders; this also
increases the eﬃciency and output of the turbine. Additionally, fractions of the expanding steam (extracted
from the turbine at certain locations along the expansion line) are used to preheat the feedwater stream ﬂowing
from the condensate tank and towards the steam generator , in order to further enhance the eﬃciency of the
power block. Increasing the feedwater temperature at the inlet to the steam generator has the additional beneﬁt
of increasing the temperature of the heat transfer ﬂuid (whether molten salts or thermal oil), hence reducing
the risk of freezing events and/or minimising pumping power in the solar ﬁeld.
A typical steam cycle is shown in Figure 15 where the reheat and preheating section are easily identiﬁed. The
main performance and operating parameters of the cycle, depending on the type of concentration technology,
are also shown in Table 2.
Figure 15: Layout of the power cycle in a state-of-the-art Concentrated Solar Power plant.
4.5 Transient operation mode and control strategies of the steam cycle
In order to maximize the performance and proﬁtability of the power plant, it is essential to optimize the
performance when operating in partial load. Therefore, the steam turbine must be designed for:
•daily start-up and shutdown;
•rapid start-up times.
Review of Power Block 29Review of Power Block 29Review of Power Block 29
Parameter Parabolic trough Central receiver
Net maximum output power (MWel) 200 150
Net eﬃciency (%) 37 41
Inlet temperature steam turbine (oC) 383-388 545-555
Inlet HP steam turbine (oC) 120-130 120-150
Extraction number of the steam turbine (-) 6 6-7
Condensation pressure, dry cooling (mbara) 80-120 80-120
Table 2: Operating and performance parameters of a steam power cycle in CSP applications.
The daily start and stop manoeuvres of CSP plants is inﬂuenced by mechanical considerations strongly. In
addition, steam turbines are subject to high thermal stresses during transient operation, which occurs frequently
owing to the variability of solar radiation. In this regard, Thermal Energy Storage, for instance based on molten
salts, provides themal power supply even when sun rays are not available. This increases the number operating
hours signiﬁcantly, either at full or partial load, and even enables continuous operation during the night. As
long as the economics make sense, this largely reduces the consumption of energy that is needed to keep the
facility warm (hence avoiding freezing in critical sections containing molten salts), to generate steam in the
auxiliary boiler and to preheat the cycle before start-up during sunrise in a sunny day.
Regarding the best control strategies of steam cycles, sliding pressure is the optimal turbine control strategy
in a Concentrated Solar Power plant. When this mode is used, the following counteracting eﬀects are balanced
in the best possible way:
•the thermal eﬃciency of the cycle is reduced because live steam pressure decreases;
•the thermal eﬃciency of the heat exchange process in the steam generator is enhanced;
•the blading eﬃciency of the steam turbine remains approximately constant, in particular the ﬁrst stages.
As a result of this, the performance decay incurred when operating the power block in partial load based on
sliding live steam pressure mode is very small.
4.6 Current development trends of steam cycles in CSP plants
Presently, there are several programs aimed at encouraging technological development to lower investment
costs and LCoE of CSP plants. Regarding the power block, the steam cycle does not have much potential for
improvement with its current design. Therefore, in order to be more competitive in this section, in addition to
the development of alternative power cycles with better performance such as the supercritical Carbon Dioxide
cycle (sCO2cycle), the evolution of the conventional subcritical cycle could drift towards:
•scaling up the power block based on state-of-the-art steam technology, which would expectedly bring in
strong economies of scale;
•in addition, adopting supercritical steam cycles with an expectedly better performance and whose subse-
quent development would also be able to bring about further cost reductions.
30 Techno-Economic Status of Solar Tower Plants30 Techno-Economic Status of Solar Tower Plants30 Techno-Economic Status of Solar Tower Plants
5 Techno-Economic Status of Solar Tower Plants
Solar tower technology is a relatively new technology. So far, there are just ten solar tower power plants
in operation worldwide . Nevertheless, the experience accumulated to date is promising, and several other
projects are under construction (such as Cerro Dominador in Chile, a molten salt tower with 10600 heliostats
and a huge storage capacity equivalent to 17.5 operating hours at full capacity). A more detailed list of the
solar tower plants in the world, either in operation or in the planning and construction phase, can be found in
Table 3. As easily deduced from the list, the number of solar tower plants in operation is substantially lower
than the number of working parabolic through power plants, even though the eﬃciency of the latter is lower
than of the solar tower plants. This diﬀerent level of development is due to some key aspects that solar tower
technology must improve to become fully competitive:
•High costs of key components owing to the few Original Equipment Manufacturers that are producing
•High ﬁnancial costs, due to the incipient commercial deployment.
•Low reliability as experienced by some of the plants currently in operation.
•Economies of scale not yet achieved and fully exploited.
The foregoing bullet points are being targeted by both the industry and the R&D community, providing
promising results and improvements at a very high pace. The sector is actually under an intense developing
period, and the associated electricity prices are decreasing. Noor III Project has reached the best economic
performance ever achieved by CSP in terms of USD/MWh, and it is expected that solar tower projects will
achieve even lower values in the near future, as represented in Figure 16. Interestingly, Central Receiver Systems
(CRS) have the largest potential for cost reduction potential due to the lower maturity (total installed capac-
ity), as opposed to parabolic trough technology, to the lessons learnt in currently operational plants and to the
capability to reduce the ﬁnancial constraints. In this latter regard, increasing the reliability of the plants is a
mandatory, crucial step. Speed-up of the ramping up/down capacity and design and operation learning curves
are taking longer than expected and this, when coupled to the not so high plant performance, has produced a
lack of conﬁdence on the technology as perceived by the potential end-users. In order to revert this situation,
the lessons learnt in the plants that are currently in operation have to be applied in the next projects that are
already in the pipeline, thus recovering the trust of the potential end-users and contributing to making CSP
become a cost-eﬀective and reliable solution. By de-risking the CSP projects, lead lenders will become more
conﬁdent and the ﬁnancial costs will decrease substantially. These expectations are also shared by IRENA, as
it can be seen in Figure 17. The costs of all renewable technologies are decreasing, but the highest reduction
foreseen is for Concentrated Solar Power.
This foreseen reduction needs to be achieved thanks to the combination of diﬀerent strategies: cost reduc-
tion of the key components, new developments, new improvements, improving the supply chain, utilization of
local manufacturing, build-up of the demand, new monetizing strategies, etc. The cost of the key components
will be reduced by achieving mass production when more projects are constructed, but more R&D actions in
the solar ﬁeld and molten salt components are also necessary in order to adapt both elements to the market
needs. Both components have an important share in the total budget of a solar tower power plant, and any
improvement or cost reduction of these components largely beneﬁts the total cost of the plant. Also, improving
cycle performance, i.e. achieving higher eﬃciency, is a goal to be achieved is a bright future is sought for solar
tower technology. With a higher power block eﬃciency, the size of the solar ﬁeld that is needed for a given
power output is reduced and, with it, the total cost of the plant. This cycle improvement can be accomplished
by upgrading the contemporary steam cycles or by adopting new power cycles such as the sCO2cycle discussed
later in this document (and adopted by SCARABEUS). Moving to a new cycle is nevertheless not an easy
task, and it must hence be analyzed in detail prior to its implementation in a commercial plant; to this end,
an important R&D eﬀort is needed. Improving the supply chain and using local manufacturing is a common
Techno-Economic Status of Solar Tower Plants 31Techno-Economic Status of Solar Tower Plants 31Techno-Economic Status of Solar Tower Plants 31
Figure 16: Total installed costs of CSP plants by technology and storage capacity .
Figure 17: Levelized Cost of Electricity of diﬀerent projects and globally-weighted average for diﬀerent renewal
strategy for several industries which is also applicable to CSP, even if with some diﬃculties due to the highly
skilled workforce that is needed by solar tower plants, which implies training the local industries to be able to
produce and deliver with the strict standards used by the CSP industry. Besides this, the foreseen increase in
32 Techno-Economic Status of Solar Tower Plants32 Techno-Economic Status of Solar Tower Plants32 Techno-Economic Status of Solar Tower Plants
the demand for this technology will also increase the number of providers, therefore reducing the cost thanks
to both the exploitation of economies of scale and the development of new manufacturing techniques and pro-
cedures, accompanied by standardisation eﬀorts.
Economies of scale will help reduce the costs but it will also pose a series of challenges. As a matter of fact,
the logistics for an actual solar tower power plant are quite complicated. Only for the solar ﬁeld, more than
thirty trucks arrive to the site on a daily basis, and some large components have to be transport assembled, with
large slow trucks that could aﬀect the normal utilization of roads negatively, hence requiring traﬃc control and
the involvement of transport authorities. For a scaled-up project, these problems will do nothing but increase
in severity. Therefore, in order to avoid increasing the logistic-related costs, a detailed monitoring of the solar
product suuply chain must be applied.
At the moment, one of the most common ways of monetizing a solar tower plant is through a power pur-
chase agreement (PPA), which sets a ﬁxed selling price of the energy produced by the plant. These agreements
usually last for 25 years, leading to uncertainty about how the plant will be exploited afterwards. Hence, if the
actual lifetime of solar tower plants were considered, an extended period of 35 years could improve the ﬁnancial
model, even if the costs of the components could rise as a result of the new maintenance contracts and guarantee
provided by the suppliers.
Finally, the actual value of the CSP concept must be updated in order to account for the ﬂexible dispatching
strategies that are provided by the Thermal Energy Storage system. A monetization strategy able to correctly
evaluate the ﬂexibility of this technology over other non-dispatchable renewable technologies such as PV or wind
should be implemented. This claim is already considered in the last reports of the International Energy Agency
, where a large increase in PV and wind power apacity is expected, and a cap on renewable is foreseen.
To attenuate the eﬀects of this cap, the dispatchable CSP+TES is expected to grow exponentially, providing
ﬂexibility to the generation mix of the grid, as shown in Figures 18 and 19.
Figure 18: Conceptual daily energy mix with PV and CSP, medium term (left) and long term (right) .
Figure 19: PV and CSP generation in the Sustainable Development scenario. 
Techno-Economic Status of Solar Tower Plants 33Techno-Economic Status of Solar Tower Plants 33Techno-Economic Status of Solar Tower Plants 33
The increase in demand in addition to the improvements achieved by innovation actions and a new monetiz-
ing system able to account for the dispatchability of CSP plants will prove the good health of this technology,
needed to proceed to a complete decarbonization of electricity generation without losing the capability to adapt
to an increasingly ﬂuctuating demand.
In the mid term, diﬀerent pathways are under evaluation with the challenge of making CSP cost-competitive.
The ”Gen 3 CSP roadmap”  deﬁnes three paths for solar tower technology development to achieve a goal
6¢/kWh: the Molten Salts path, the Falling Particle path and the Gas Phase path. The three of them are
being explored in depth and a lot of innovation eﬀorts are being dedicated to them, with diﬀerent diﬃculties
to be overcome as shown in Figure 20. One common particularity to all three paths is the use of a supercritical
CO2Brayton cycle, described in subsequent sections. The several challenges that this paths pose call for an
important eﬀort from the authorities and all the related stakeholders to successfully bring this Gen3 CSP power
plants from the R&D phase to a commercial reality.
Figure 20: Gen3 roadmap for solar tower technology .
34 Techno-Economic Status of Solar Tower Plants34 Techno-Economic Status of Solar Tower Plants34 Techno-Economic Status of Solar Tower Plants
Project name Location Capacity HTF Status Developer TES type TES
DEWA CSP Tower Project UAE 100 Molten Salt Under construction ACWA Power 2-tank direct 15
Planta Solar 10 Spain 11 Water/steam Operational Abengoa Solar Steam accumulator 1
Planta Solar 20 Spain 20 Water/steam Operational Abengoa Solar Steam accumulator 1
Crescent Dunes United States 110 Molten Salt Operational SolarReserve, LLC 2-tank direct 10
Ivanpah Solar United States 392 Water/steam Operational BrightSource Energy None -
Cerro Dominador Chile 110 Molten Salt Under construction Abengoa Solar 2-tank direct 17.5
Noor III Morocco 150 Molten Salt Operational ACWA Power 2-tank direct 7
Huanghe Qinghai Delingha China 135 Water/steam Non-operational BrightSource Energy 2-tank indirect 3.7
Luneng Haixi China 50 Molten Salt Operational SEPCO3 2-tank direct 12
SunCan Dunhuang China 100 Molten Salt Operational Shouhang 2-tank direct 11
Gemasolar Spain 20 Molten Salt Operational Torresol Energy 2-tank direct 15
Khi Solar One South Africa 50 Water/steam Operational Abengoa Solar Steam accumulator 2
Ashalim Israel 121 Water/steam Operational Megalim Solar Power Steam accumulator 3.7
Table 3: Current operational and under constructions solar tower power plants.
Hybridization 35Hybridization 35Hybridization 35
The share of renewable energy technologies in the global energy mix has increased in the last two decades.
There are several reasons for this, for instance the need for alternative energy sources to secure energy sup-
ply or to ﬁght rising prices of conventional energies in certain regions, the need to mitigate climate change
and the need for a global approach to sustainable development which can eliminate local (and not only global)
CO2emissions. For these reasons, these technological developments focused on clean energy must be accelerated.
Regarding solar energy, it is widely acknowledged that it is the most abundant energy source on earth and
it can be exploited cost-eﬀectively. Photovoltaic technology is cheap, modular and it can be used virtually any-
where. However, one of its main shortcomings is that it is a highly intermittent form of power generation. This
brings about issues regarding grid stability. Electric energy storage can be added to improve dispatchability
but it is currently too costly to be used at the large scale. Concentrated Solar Power also converts solar energy
into electricity and it is also an intermittent form of generation, but it has the added value of dispatchability
when combined with thermal energy storage. TES systems are a cost-competitive solution to seamlessly balance
energy demand and supply in the grid. In this sense, hybridization of photovoltaic and CSP technologies yields
a complementary power generation technology which exhibits the best features of each constituent. In term of
ﬂexibility, a certain proportion of CSP with a high thermal storage capacity allows maximum penetration of
PV at a more than acceptable cost and with lower curtailment. Therefore, the new hybrid plant combining
low-cost renewable energies technologies such as PV or wind, with batteries for fast response, and CSP with
TES for long-term dispatchability would be a new hybrid product with a strong potential for cost reduction in
solar power generation.
Such hybridization is key in order for these technologies to gain a competitive advantage against traditional
powe generation based on fossil fuels. A so-called smart solar plant would satisfy a given generation proﬁle
during both day and night: the energy generated during the day would come from a highly cost-competitive
photovoltaic ﬁeld whilst, in the evening -when a second peak demand with high prices of electricity must
be expected-, the solar thermal plant with storage capacity would go into operation. These are ﬂexible and
dispatchable plants that can adapt to the energy demand and where resources are optimized to yield lowest
operation and maintenance costs, Figure 21.
This hybrid concept is already under-construction in the Atacama Desert, Chile. The Cerro Dominador
power plant, property of EIG Global Energy Partners and developed and constructed by Abengoa and Acciona,
will have the capacity to operate at full load (110 MW) continuously (24 hours a day), thanks to a hybrid mix
of technologies (CSP / PV / TES /BESS). This unprecedented operating capability is shown in Figure 22.
Diﬀerent strategies are available for a hybrid CSP plant to exploit power generation economically. One of
these is base-load production, presented in Figure 22. Another option would be to concentrate power generation
in peak demand periods (where revenues are higher). In this case, the PV system would produce a signiﬁcant
amount of (excess) power that could be stored in the TES system. To accomplish this, an electric heater would
be integrated in the plant with low additional technical and ﬁnancial eﬀorts. The electric heater would trans-
form the excess electricity into thermal energy, which would then be stored in the Thermal Energy Storage CSP
if storage capacity were still available. This could also be implemented with electricity originated in a wind
farm, as shown in Figure 23.
The ﬁrst electric heaters for a CSP plant are going to be installed in the recently awarded Noor Midelt I
project in Morocco, at an aﬀordable cost. The successful demonstration of this solution is very important since
these components can easily be integrated not only in new plants but also in existing plants. This is thanks to
the very strong modularity of the heaters, which enable easy retroﬁtting in existing facilities.
36 Hybridization36 Hybridization36 Hybridization
Figure 21: Hybrid CSP-PV-BESS-TES conﬁguration by Abengoa c
Figure 22: Base-load generation proﬁle of Cerro Dominador, Chile
Aside from the utilization in CSP plants, the integration of molten salt storage, electric heaters and steam
generators (operated on molten salts) can provide new life to fossil-fueled or nuclear power plants which would
otherwise be dismantled, transforming theses plants into strategic energy reserves for the grid. In this conﬁgu-
ration, during low demand or low energy price periods, the electric heater would store the excess electricity in
the form of thermal energy. Then, when demand of electricity were higher or during growing demand periods,
this energy would be used to produce steam that would eventually run the steam cycle of the cited power
plants. There are several other possibilities for this technology, such as the integration with conventional coal
plants, where steam generation based on molten salts would have the potential to either accelerate start-up by
providing thermal energy during to the slower coal boiler, or to use this energy for the production of process
heat, hence contributing solutions adapted to the needs of strategic sectors such as the mining, chemical and
Hybridization 37Hybridization 37Hybridization 37
Figure 23: Utility-scale solar+storage competing with new peaker plants (PV/W+CSP+TES+BESS+Heater)
by Abengoa c
Figure 24: Working principle of the Midelt Noor I plant by TSK Flagsol c
Figure 25: Decarbonization solution oﬀered by Abengoa c
38 Power Block based on supercritical CO2cycles38 Power Block based on supercritical CO2cycles38 Power Block based on supercritical CO2cycles
7 Power Block based on supercritical CO2cycles
7.1 Origins of the supercritical CO2cycles
Most of the thermodynamic cycles using Carbon Dioxide at supercritical or transcritical pressure and temper-
ature that have been studied by the scientiﬁc community in the last years and, more speciﬁcally, those which
have been implemented in the few experimental loops available derive from the initial proposals of Angelino
and Feher [110, 111]. For this reason, and in order to better understand the evolution of sCO2technology, it is
worth starting from a comprehensive review of their work.
Angelino proposed several conﬁgurations of condensation (transcritical) cycles for intermediate temperature
applications , able to achieve similar or even higher eﬃciency than Rankine cycles using steam turbines
but with the simplicity of Brayton cycles (gas turbines). The original simple, transcritical condensation cycle
proposed by Angelino experienced a number of modiﬁcations in order to reduce the destruction of exergy in
the recuperators, the most eﬀective of which proved to be splitting the low temperature, low pressure ﬂow
in parallel streams following diﬀerent thermodynamic pathways. This modiﬁcation eventually produced the
Recompression cycle which has been recognised as one of the most interesting embodiments of the supercritical
CO2cycle . Another interesting modiﬁcation of the cycle proposed by Angelino targets the expansion
process with the objective to provide ﬂexible turbine back-pressure (pressure ratio) regardless of condensation
pressure at low temperature (near compressor inlet). This was implemented in the Partial condensation with
precompression cycle and, more recently, the Partial Cooling cycle. A very detailed review of the historical
evolution of supercritical CO2cycles was recently published by Crespi et al. .
Along with the research carried out by Angelino in Europe, Edward Feher studied alternative power cycles
which could potentially improve the performance of state-of-the-art Rankine and Brayton cycles in United States
. Feher found that, lying in between them, supercritical cycles could overcome some of the limitations
experienced by Rankine and Brayton cycles:
–Peak operating temperature.
–Wet expansion, therefore internal losses.
–Very large volumetric expansion ratio and shaft work, bringing about a large number of turbine
stages with complex geometries in the gas path.
–Large compression work (ﬂuid behaves close to ideal gas).
–Strong sensitivity to pressure losses and compressor eﬃciency.
–Large size of heat transfer equipment due to large speciﬁc volume.
The conclusions drawn from Feher’s work were similar to those obtained by Angelino in , for both the
supercritical and transcritical sCO2cycles. Higher eﬃciency than in conventional Brayton and Rankine cycles
with moderate turbine inlet temperatures (from 600 to 1000oC) seemed possible, in spite of the oversimpliﬁcation
of their basic thermodynamic analysis. Some later studies, in fact, declared that a correction factor lower than
unity should be applied to the eﬃciency estimated by these authors, in addition to accounting for auxiliary
power consumption (neglected in the cited seminal works) .
Power Block based on supercritical CO2cycles 39Power Block based on supercritical CO2cycles 39Power Block based on supercritical CO2cycles 39
7.2 Fundamentals of the supercritical CO2cycle and comparison against gas and
The working principle of a gas turbine is based on the Brayton cycle, patented in 1874 by George Brayton upon
the conceptual development of John Barber in 1791. The ideal (simple) Brayton Cycle, shown in Figure 26,
is comprised of two isentropic processes, compression ( ¯
12) and expansion ¯
34, and two isobaric processes, heat
23 and rejection ¯
41. A standard gas turbine drags atmospheric air in (1) and increases its pressure in
the compressor (2). This is air is then heated up through combustion of natural gas (3) and, ﬁnally, combustion
gases are expanded down to atmospheric pressure again (4). The heat rejection process is not performed in any
component of the engine but merely by exhausting gases to the environment and dragging fresh air in again.
Figure 26: Brayton cycle. Temperature-entropy and pressure-volume diagrams.
The thermal eﬃciency of an ideal Brayton cycle depends on pressure ratio as follows:
ηBr,i = 1 −1
P R k−1
= 1 −1
where kis the isentropic exponent. δis usually termed pseudo pressure ratio for simplicity. Nevertheless,
an actual engine is not made up of isentropic compression and expansion but, rather, non-reversible pressure
change. If this is considered, whilst still considering that heat addition and rejection are carried out at constant
pressure, and neglecting the impact of composition and temperature changes on ﬂuid properties, the thermal
eﬃciency of the engine is expressed as follows:
where ηcand ηtare the isentropic eﬃciencies of compressor and turbine and θ=T03/T01 is the ratio from
highest to lowest cycle temperature (tempreature ratio).
Figure 27 shows the inﬂuence of the pressure and temperature ratios on thermal eﬃciency and speciﬁc
work. Thermal eﬃciency increases with pressure ratio but, beyond a certain optimum pressure ratio, cycle
performance deteriorates. This is due to the increasing share of turbine work that is taken by the compressor,
as shown in Figure right. Once the pressure ratio for peak eﬃciency is achieved, the only means of increasing
cycle eﬃciency further is by increasing temperature ratio (i.e., turbine inlet temperature), which is equivalent
to increasing expansion work whilst keeping compression work constant.
Compression work of a ﬂuid can deﬁned as follows:
40 Power Block based on supercritical CO2cycles40 Power Block based on supercritical CO2cycles40 Power Block based on supercritical CO2cycles
Figure 27: Brayton cycle performance. Inﬂuence of design parameters.
where the second equality makes use of the compressibility factor Z: ratio from the speciﬁc volume of a ﬂuid
at given pressure and temperature to speciﬁc volume of the same ﬂuid at the given pressure and temperature if it
behaved like an ideal gas. This equation suggests a new way to rise thermal eﬃciency by reducing compression
work, in those applications where it is not possible or economically not interesting to increase turbine inlet
temperature. Reducing the compressibility factor at the beginning of the compression process enables higher
eﬃciency and also other beneﬁcial features:
•The fraction of turbine work that is used to drive the compressor is lower, meaning a higher resistance to
pressure losses in the cycle.
•For given ﬂow rate, the compressor is more compact thanks to the lower speciﬁc volume of the working
This concept can be taken further if condensation is adopted, as it is done in a Rankine cycle. Nevertheless,
such cycle would present the following shortcomings as currently identiﬁed by the indstry and the scientiﬁc
•The working ﬂuid (demineralized water) is expensive.
•The maximum inlet temperature of a modern steam turbine is not higher than 600oC, maybe 650oC
in some experimental units. This values are very fram from the typical turbine inlet temperatures of
contemporary gas turbines.
•A large section of the cycle operates under vacuum conditions, making it necessary to expel non-condensable
gases from the installation.
•The speciﬁc volume of the working ﬂuid in the low-pressure section of the cycle is very large, bringing
about very large and bulky equipment which increase the capital cost of the plant.
•The need for feedwater heating increases the capital cost and footprint of the plant.
It is therefore seen that reducing compression work as in a Rankine cycle leads to other technical and eco-
nomic shortcomings, thus creating counteracting eﬀects which can be best balanced by supercritical CO2cycles.
The introduction of the concepts presented in this section leads to a number of supercrtcal CO2cycles
whose performance is competitive against connventional Rankine and Brayton cycles under certain operating
parameters. This is shown in Figure 28 [110, 114], which yields the following conclusions:
•For turbine inlet temperatures lower than 1000oC, supercritical CO2cycles are more eﬃcient than Brayton
cycles operating on ideal gas.
Power Block based on supercritical CO2cycles 41Power Block based on supercritical CO2cycles 41Power Block based on supercritical CO2cycles 41
•For turbine inlet temperatures higher than 650oC, these cycles are also more eﬃcient Rankine cycles
operating on water/Steam.
•Supercritical CO2cycles have the potential to reach 60% therml eﬃciency for turbine inlet temperatures
lower than 1000oC.
The analyses of Angelino and Feher built the foundation of the technology but were soon interrupted. It was
not until the beginning of the twenty ﬁrst century when the interest in the technology was reborn. Amongst the
new cycle proposals though, only a few of them are worth noting, in particular the Allam cycle . This is a
transcritical power cucle working between 37 and 300 bar and with condensation at supercritical pressure. The
developers of the technology announce 59% thermal eﬃciency at 1150oC and the availability of pipeline-ready
carbon dixoide for storage; however, the need to produce oxygen for the oxycombustion process still poses some
questions regarding the business case of such power plant.
Figure 28: Comparison of supercritical CO2, air Brayton and water/steam Rankine cycle. Condensing and
non-condensing cycles are considered [110, 114].
The exhaustive review of Crespi et al. provides an excellent overview of the current state-of-the-art of
supercriticao CO2power cycles for power generation from diﬀerent primary energy sources, including solar
energy . A summary of the expected performance is presented in Figure 29 where the large variability
of declared performances and an upper limit of cycle eﬃciency for a given turbine inlet temperature can be
7.3 Candidate sCO2cycles for CSP-STE applications
This section is based on the available scientiﬁc literature in the topic of supercritical CO2cycles for power
generation, either speciﬁcally for Concentrated Solar Power applications or for a general purpose. The most
representative cycles proposed in literature are reviewed and their suitability for CSP-STE plants is discussed.
•Simple Recuperated and Transcritical:
This cycle aims to counterbalance the the high compression work and large heat transfer area of conven-
tional Brayton cycles, brought about by the low speciﬁc volume of the working ﬂuid. The lower speciﬁc
work needed to compress CO2near the critical region, and the larger temperature diﬀerence between
compressor delivery and turbine exhaust that enables a much larger heat recovery potential, bring about
a higher thermal eﬃciency of the cycle. On the negative side, the variability of the thermodynamic prop-
erties of the working ﬂuid near the critical point limit the eﬀectiveness that low temperature recuperators
42 Power Block based on supercritical CO2cycles42 Power Block based on supercritical CO2cycles42 Power Block based on supercritical CO2cycles
Figure 29: Inﬂuence of turbine inlet temperature on thermal eﬃciency, based on a literature survey. Diﬀerent
cycle layouts and applications are considered.
can achieve, therefore limiting the theoretical thermodynamic potential of the cycle.
The Transcritical CO2follows the same concept as the Simple Recuperated cycle but based on a pseudo-
Rankine cycle [116, 117, 118, 119]. This is a suitable conﬁguration for low-temperature waste heat recovery
applications and, therefore, it can also be used in combined cycle power plants.
Figure 30: Simple Recuperated Cycle (Right) and Transcritical Cycle (Left) layouts.
This is an oxy-combustion cycle that burns natural gas (or syngas) with pure oxygen. It achieves high
thermal eﬃciencies and provides pipeline-ready CO2without the need of an additional absorption process,
but this is at the cost of having a large Air Separation Unit producing oxygen for the combustion process.
The Allam cycle is highly recuperative cycle and exhibits a tight thermal integration between the power
cycle and the Air Separation Unit which enhances the overall performance of the plant. The fact that
combustion gases are comprised of carbon dioxide and water steam only (except for traces of other gases)
enables CO2capture through cooling/condensation only.
The Brayton sCO2GT cycle is a common reference to the Intercooling II cycle based on the Simple
Recuperated layout with intercooled compression. Originally proposed for nuclear applications, it is now
considered for Concentrated Solar Power.
This cycle was developed by Mathieu and Iantovski. Akin to the Allam cycle, it is based on oxycombustion
and incorporates three expanders and one reheater. The Matiant cycle enables capturing pipeline-ready
CO2by mere condensation.
•Forced Cooler Cycle:
The Forced Cooler cycle is also based on the Simple Recuperated layout with the incorporation of an
intercooler and a reheater. The name is justiﬁed by the additional cooler , known as Forced Cooler, which
Power Block based on supercritical CO2cycles 43Power Block based on supercritical CO2cycles 43Power Block based on supercritical CO2cycles 43
Figure 31: Allam Cycle (Right) and Brayton sCO2GT Cycle (Left) layouts.
is found between the standard cooler and the ﬁrst compressor. The Forced Cooler is cooled by a two-stage
vapor-compression refrigeration cycle with a ﬂash chamber, using R134-a as working ﬂuid.
Figure 32: Matiant Cycle (Righ) and Forced Cooler Cycle (Left) layouts.
This cycle is also based on the Simple Recuperated layout where an ejector is added just before the heater.
The outlet stream of the heater is then divided in two: the ﬁrst fraction is expanded and then ﬂows into
the recuperator. The remaining fraction is expanded in the second turbine and then sent to the ejector for
mechanical compression. The addition of this ejector can potentially lead to a higher thermal eﬃciency,
according to the authors .
The RC-EJ cycle is similar to the S-EJ conﬁguration but, in this case, based on a Recompression cycle
assisted by an ejector. This conﬁguration is characterized by the same features as the S-EJ (ejector) and
Recompression (split-ﬂow) cycles.
The MC-EJ cycle is the third conﬁguration proposed by Vasquez . It is also based on the Recompres-
sion cycle assisted by an ejector, as in the RC-EJ cycle, but with the addition of intercooling in the main
compression line. It exhibits the same characteristics as the RC-EJ cycle plus a reduction of compression
work thanks to intercooling.
•Inter-recuperated & Recompression:
The Inter-recuperated is similar to the Simple Recuperated cycle, except for the recuperating process
which is comprised of two recuperators.
Based on this cycle, Angelino proposed the Recompression cycle, with a clear connection to Feher’s work.
The low-pressure ﬂow at the outlet from the low-temperature recuperator is split in two. One fraction is
cooled down further in a cooler and then compressed in the main compressor at the outlet from which
the ﬂow is sent to the high-pressure side of the low-temperature recuperator. The second fraction is
44 Power Block based on supercritical CO2cycles44 Power Block based on supercritical CO2cycles44 Power Block based on supercritical CO2cycles
compressed in the re-compressor and then joins the former stream at the outlet from the low-temperature
recuperator, on the high-pressure side. The resulting stream is then sent to the high-pressure side of the
This conﬁguration is aimed at reducing the mass ﬂow rate of CO2on the high-pressure side of the low-
temperature recuperator thus overcoming the internal pinch point problem brought about by the variability
of CO2properties in the vicinity of the critical point. This yields higher LT recuperator eﬀectiveness and
therefore higher cycle eﬃciency. The Supercritical Recompression layout is the most extensively researched
cycle in literature along with the Supercritical Simple Recuperated.
•Partial condensation & Precompression:
The Precompression cycle based on the partial condensation cycle with precompression proposed by
Angelino. It aims to release the constraints posed on the low and high cycle pressures: when compressor
inlet pressure is increased to supercritical values, either the expansion ratio is reduced (lower speciﬁc work)
or turbine inlet pressure increases to prohibitive values (more complex and expensive mechanical design).
Figure 33: Recompression Cycle (Right) and Precompression Cycle (Left) layouts.
•Recompression+IC+RH & Partial Cooling+Reheating:
This layout is aimed at improving the performance of the Recompression and Partial Cooling cycles
by merely adding multi-stage intercooled compression and reheated expansion processes. The beneﬁts
provided by these conﬁgurations are the same as previously discussed for their standard conﬁgurations
•Double Reheated Recompression:
This conﬁguration adds a second reheater to the conﬁguration proposed by Moisseytsev. Additionally,
Mecheri and LeMoullec proposed to separate a fraction of the main ﬂow downstream of the main com-
pressor, before the low-temperature recuperator. After this separation, the split fraction would be heated
up in another heater and re-injected before the high-temperature recuperator. The aim of this ﬂow split
is to overcome the usual pinch-point problems and associated irreversibility in the internal heat recovery
•Cascade Supercritical CO2:
The Cascade conﬁguration is actually a Recompression cycle where a ﬂow-split valve is added downstream
of the low-temperature recuperator. Both fractions follow the layout of a Simple Recuperated cycle
and rejoin upstream of the low-temperature recuperator. This cycle was included in the sCO2cycle
development programme at Pratt Whitney Rocketdyne for solar thermal applications. Thanks to this
conﬁguration, it is possible to recover heat from the solar plant using two heaters, thus better ﬁtting the
large temperature change that is typical of this technology.
•Schroder-Turner: The Schroder-Turner cycle is a highly recuperative cycle, based on the Partial Cooling
layout but with an improved heat recovery system incorporating three compressors and a single turbine.
There is a way to simplify the complex conﬁguration, by removing the low-temperature recuperator.
Power Block based on supercritical CO2cycles 45Power Block based on supercritical CO2cycles 45Power Block based on supercritical CO2cycles 45
•Quasi-Combined: The Quasi-combined system is an oxycombustion cycle proposed by Zhang and Lior.
As in the Partial Cooling cycle, the ﬂow is split into two streams downstream of the ﬁrst compressor.
The ﬁrst stream is condensed in an LNG evaporator, and then pumped and heated in the low and inter-
mediate temperature recuperators. This stream is then expanded in a high-pressure turbine and heated
to a higher temperature in a high-temperature recuperator before rejoining the second stream (as in the
Matiant cycle). This second stream is compressed after the ﬂow-split valve, heated up in the intermediate
temperature recuperator and ﬁnally mixed with the ﬁrst stream. The resulting stream is heated to the
peak cycle temperature in oxycombustor with methane and pure oxygen (from an Air Separation Unit)
and the combustion gases are expanded in the low-pressure turbine.
The name Quasi-combined derives from the fact that the sCO2and H2O stream coming from the low-
pressure turbine and ﬂowing towards the water separator and CO2compression lines serve as heat source
(”topping cycle”) for the pure sCO2ﬂow that acts as the corresponding Rankine-like ”bottoming cycle”.
7.4 Expected thermal performance of CSP-STE power plants based on sCO2cy-
For the conﬁgurations considered in the previous section, the dependence of speciﬁc work and thermal eﬃciency
on pressure ratio and turbine inlet temperature is now analyzed. The aim is to separate the thermodynamic
potential of each cycle from the pressure and temperature limits posed by mechanical integrity and technical
availability. Temperatures lower than 550oC are not considered, given that Angelino itself claimed that sCO2
cycles are able to achieve eﬃciencies higher than (steam) Rankine cycles only if turbine inlet temperature is
signiﬁcantly higher than 550oC .
The performances of the cycles presented in the preceding section are provided below for four diﬀerent tur-
bine inlet temperatures -550, 750, 950 and 1150oC- and variable turbine inlet pressures, Figure 34. The lower
boundary is set to 550oC, as suggested by Angelino, whilst the maximum temperature is set to a reasonable
value based on the current heat exchanger temperature capabilities. Cycle pressures are varied from almost no
compression to the pressure ratios implying unfeasible inlet temperatures to the heat exchangers. These pres-
sure limits do change from cycle to cycle, as they are strongly dependent on the conﬁguration of the recuperators.
(a) ηth vs Wsfor Simple Recuperated Cycle (b) ηth vs Wsfor Transcritical CO2Cycle
Figure 34: Performance of Simple Recuperated and Transcritical CO2cycles .
Black markers in Figure 34 correspond to cycles where peak pressure is not higher than 40 MPa whereas
white markers indicate that the peak cycle pressure is above this value. This transition value is higher than the
46 Power Block based on supercritical CO2cycles46 Power Block based on supercritical CO2cycles46 Power Block based on supercritical CO2cycles
values usually employed in literature, 25-30 MPa [122, 115] but still representative of next generation power
plants. As a matter of fact, supercritical steam power stations demostrated that operation at 35MPa was possi-
ble as early as 1960 , and this pressure level is expected in next generation ultra-supercritical steam power
(a) ηth vs Wsfor the Precompression cycle (b) ηth vs Wsfor the Recompression CO2cycle
Figure 35: Performance of the Precompression and Recompression CO2cycles .
The pressure labels reported in Figure 34 correspond to the ﬁrst and last calculations (i.e., cycles with
minimum and maximum peak pressure) and to the live steam pressure for which peak thermal eﬃciency and
peak speciﬁc work are achieved. In some cases though, the last value is not reported if associated to unfeasible,
very high pressure ratios).
(a) ηth vs Wsfor the Recompression+IC+RH cycle (b) ηth vs Wsfor the Partial Cooling CO2cycle
Figure 36: Performance of the Recompression+IC+RH and Partial Cooling cycles .
Even though the shape of the ηth vs. Wsplots changes signiﬁcantly from one conﬁguration to another, there
are visible similarities between cycles with similar thermodynamic (or topological) characteristics. For instance,
the Recompression+IC+RH and Double Reheated Recompression layouts are based on the Recompression cycle
and they show similar patterns in Figures 35(a), 36(a) and 38(a).
Some common features of the plots are:
•At low turbine inlet temperature, the plots have a more circular shape. When this temperature increases,
they turn elliptical and ﬂatter.
•Most cycles achieve peak thermal eﬃciency and speciﬁc work at pressures higher than 40MPa when
turbine inlet temperature is higher than 550oC. If this temperature is lower, it is unsure whether or not
Power Block based on supercritical CO2cycles 47Power Block based on supercritical CO2cycles 47Power Block based on supercritical CO2cycles 47
(a) ηth vs Wsfor the Partial Cooling+RH cycle (b) ηth vs Wsfor the Schroder-Turner cycle
Figure 37: Performance of the Partial Cooling+RH and Schroder-Turner cycles .
peak eﬃciency is achieved within the feasible pressure range. This is shown in Figures 34(a), 35(a), 35(b),
36(b), 37(b), 38(a), 39(b).
(a) ηth vs Wsfor the Double Reheated Recompression cycle (b) ηth vs Wsfor the Allam cycle
Figure 38: Performance of the Double Reheated Recompression and Allam cycles .
7.4.2 Compared Analysis
According to the information in the preceding sections, for some cycles it should be possible to exploit an un-
tapped thermodynamic potential for further eﬃciency increase (should higher pressures be attainable) whereas
other cycles seem to have already achieved the best performance possible for a given turbine inlet temperature;
this would nevertheless imply working at extremely high pressures (for instance, the Transcritical CO2cycle
could exceed 50% eﬃciency at 750oC turbine inlet temperature if pressures higher than 75 MPa were attain-
able). Despite this observation though, the most eﬃcient cycles (or so regarded), like the Recompression layout,
seem to have already achieved the best performance attainable for the the current turbine inlet temperatures.
Overlaying the foregoing plots yields interesting information about the relative performance of the cycles
considered at each turbine inlet temperature; this is shown in Figures 40 and 41. At 550 oC, the highest speciﬁc
work corresponds to the Allam cycle if a cap on turbine inlet pressure is set whilst the Transcritical CO2has
higher Wsif there are no pressure limits. Regarding eﬃciency, the Partial Cooling + RH and Recompres-
sion+IC+RH layouts have highest eﬃciencies (46.5 and 47.6% respectively) at turbine inlet pressures below
40 MPa whereas eﬃciency rises to a higher value (48%) for the Recompression+IC+RH cycle if this limit is
released. Globally, the Partial Cooling+RH and Transcritical CO2cycles provide a good compromise between
48 Power Block based on supercritical CO2cycles48 Power Block based on supercritical CO2cycles48 Power Block based on supercritical CO2cycles
(a) ηth vs Wsfor the Matiant cycle (b) ηth vs Wsfor the Quasi-Combined cycle
Figure 39: Performance of the Matiant and Quasi-Combined cycles .
thermal eﬃciency and speciﬁc work.
(a) Comparison of cycles operating at TIT=550 oC. (b) Comparison of cycles operating at TIT=750 oC.
Figure 40: Comparison of cycles operating at TIT=550 oC and TIT=750 oC .
Turbine inlet temperature has a very strong inﬂuence on thermal eﬃciency and speciﬁc work and on the
shape of the ηth vs. Wsplots. For instance, at 550 or 750oC, Figure 40 shows that those cycles based on
oxycombustion layouts (Matiant and Allam) have very high speciﬁc work but moderate thermal eﬃciency. On
the contrary, the Recompression+IC+RH cycle attains highest eﬃciency, 54.5 or 55.8% depending on turbine
inlet pressure limits, and the Double Reheated Recompression and Partial Cooling + RH layouts exhibit good
At the other end of the turbine inlet temperature range, 950 and 1150 oC, a signiﬁcant eﬃciency and speciﬁc
work rise is experienced, Figure 41. Indeed, thermal eﬃciencies higher than 60% seem possible if turbine inlet
pressure is limited to 40 MPa, and 65% can be exceeded at higher pressure. The drift of the plots towards
the top right region of the ηth vs. Wsis also interesting and changes the relative performance of the cycles
considered. As a consequence of this, the Precompression, Recompression+IC+RH, Partial Cooling+RH, Tran-
scritical CO2, Allam and Quasi-Combined layouts become most interesting, in particular the latter which yields
the most leveraged performance with 63% thermal eﬃciency and ∼475 kJ/kg.
As a further consideration to this comparison, Crespi et al.  investigate two of the cycles in this sec-
tion, highlighting that a) temperature rise across the solar receiver is a crucial ﬁgure of merit impacting the
economics of the system (and must therefore be taken into consideration), and b) for a given turbine inlet
Power Block based on supercritical CO2cycles 49Power Block based on supercritical CO2cycles 49Power Block based on supercritical CO2cycles 49
(a) Comparison of cycles operating at TIT=950 oC. (b) Comparison of cycles operating at TIT=1150 oC.
Figure 41: Comparison of cycles operating at TIT=950 oC and TIT=1150 oC .
temperature, higher pressure ratios increase the temperature rise across the receiver strongly, but the eﬀect on
thermal eﬃciency is uncertain as this can either increase or decrease, depending on the cycle considered.
7.5 Expected economic performance of CSP-STE power plants based on sCO2
7.5.1 Capital costs
The thermal performance of the cycles presented in the foregoing section is now complemented by an economic
assessment of the capital and energy costs of an associated Concentrated Solar Power plant making use of these
supercritical CO2power cycles. Detailed information about this techno-economic assessment can be found in
The foreseen capital cost of a 50 MWe CSP-STE power plant with 10 h Thermal Energy Storage capacity
and the speciﬁcations in Table 4 is shown in Figure 42(a), along with the cost of the power block only in Figure
42(b). In general, the overnight capital cost decreases for increasing turbine inlet pressure until a minimum
cost is achieved, and this then increases if turbine inlet pressure is increased further. The Power Block exhibits
the opposite trend, Figure 42(b); costs are higher at very lower very high pressures, and they decrease for inter-
mediate turbine inlet pressures. It is observed that most conﬁgurations achieve the minimum OCC at around
30 MPa, even if the exact value depends on the complexity of the layout (cycles with a large number of heat
exchangers are more sensitive to operating pressures due to the higher cost of this equipment)3.
Output Pmax,sCO2TIT Ts,min Ts,max TEScapacity SM
[MWel] [MPa] [oC] [oC] [oC] [h] [-]
50 30 750 480 770 10 2.4
Table 4: Speciﬁcations of reference CSP-STE plant based on sCO2power cycles
It must be acknowledged that the foregoing costs of supercritical CO2power plants incorporates an in-
evitable degree of uncertainty, as it is the case in any economic assessment of precommercial technology .
Therefore, in order to ensure that the results presented are credible, Crespi et al. also provide an assessment of
3It is worth noting that the reported costs are sensitive to the operating pressure, according to the original reference 
50 Power Block based on supercritical CO2cycles50 Power Block based on supercritical CO2cycles50 Power Block based on supercritical CO2cycles
(a) OCCs per kilowatt as a function of power cycle maximum
(b) Power block costs as a function of power cycle maximum
Figure 42: OCCs and Power Block Costs vs maximum power cycle pressure 
the impact of uncertainty in , based on the expected probability functions of diﬀerent cost items integrated
through the Montecarlo methodology. To this end, the authors rely on a similar analyses to select the appro-
priate probability distributions and ranges of each individual equipment cost, setting the number of samples to
10,000 to calculate the OCC of the plant.
This approach to calculating the probability density function of the Overnight Capital Cost per kilowatt
yields the information shown in Figure 43. This plot can be divided in three distinct regions. On the right hand
side, the Double Reheated cycle has the highest OCC-per-kW, getting up to 13000 $/kW for a 90% conﬁdence
interval. In the mid section, the Recompression+IC+RH, Schroder-Turner and Partial Cooling+RH cycles
have OCC-per-kW ranging between 8500 and 9500 $/kW for a 90% conﬁdence interval. Finally, the remaining
layouts on the left hand side show the lowest installed costs with between 5500 and 7000 $/kW for the same
conﬁdence interval. Further to the absolute values of installation costs, the plot also conﬁrms that cycles with
more complex layouts (for instance the Double Reheated cycle) experience a stronger impact of uncertainty as
a consequence of the potential changes of the cost of each component. This is symptomatic of a larger data
dispersion in the Montecarlo simulation, due to the higher relative importance of the thermal energy storage
system and the tower/receiver.
Figure 43: Cumulative probability distribution of Overnight Capital Costs per kilowatt .
Power Block based on supercritical CO2cycles 51Power Block based on supercritical CO2cycles 51Power Block based on supercritical CO2cycles 51
7.5.2 Capital cost breakdown
The capital cost breakdown of the layouts compared, for the 85% conﬁdence interval are presented in Figure 44.
The Recompression+IC+RH and Schroder-Turner layouts (e and h in Figure 44) have very large installations
costs, owing to the contributions of the thermal energy storage system and tower/receivert, and this is also
the case for the Recompression, Partial Cooling+RH and Double Reheated cycles (d, g and i respectively).
As shown in Table 5, this is due to the very low ∆Tsolar across the solar receiver, bringing about a dramatic
increase in the inventory of salts that is needed to transfer thermal energy from the solar ﬁeld to the power
cycle. For instance, the Double Reheated layout presents a ∆Tsolar of 80oC, a value three times lower than the
maximum ∆Tsolar achieved by some of the other conﬁgurations (290oC).
Figure 44: Breakdown of Capital Costs. (a) Simple Recuperated, (b) Transcritical CO2, (c) Precompression, (d)
Recompression, (e) Recompression+RH+IC, (f) Partial Cooling, (g) Partial Cooling+RH, (h) Schroder-Turner,
(i) Double Reheated, (j) Allam, and (j) Quasi-Combined .
Cycle Tin,compr Pin,compr ηth Ws∆Tsolar
[oC] [MPa] [%] [kJ/kg] [oC]
a 32 7.5 45.8 171 290
b 15 5 48.3 242 290
c 32 7.5 50.6 164 254
d 32 7.5 50.5 142 220
e 32 7.5 52.8 174 130
f 32 5 51.1 192 290
g 32 5 53.0 210 157
h 32 5 52.8 159 80
i 32 7.5 49.0 200 160
j 32 3 45.0 252 290
Table 5: Thermal performance of the cycles considered.
More complex layouts enable higher eﬃciency which, in turn, reduces the cost of the solar ﬁeld (e,g,h,i).
Unfortunately, this is at the cost of a higher cost of the power block and other subsystems of the plant (for
instance, the thermal energy storage system), which, in some cases, more than oﬀsets the previous saving.
Conversely, simpler cycles imply lower costs of the power block and, also, larger and more expensive solar ﬁelds
(b,j). This is all seen in Figure 45 where a breakdown of the power block cost is provided, showing the impact
of the number of turbomachines and of the very expensive heater whose cost is tightly linked to |DeltaTsolar .
52 Power Block based on supercritical CO2cycles52 Power Block based on supercritical CO2cycles52 Power Block based on supercritical CO2cycles
The latte feature can be inferred from the paralell trends of TES and heaters costs, yellow bars in Figures 44
and 45 respectively
Figure 45: Breakdown of Capital Costs of the power block. (a) Simple Recuperated, (b) Transcritical CO2, (c)
Precompression, (d) Recompression, (e) Recompression+RH+IC, (f) Partial Cooling, (g) Partial Cooling+RH,
(h) Schroder-Turner, (i) Double Reheated, (j) Allam, and (j) Quasi-Combined .
The thermodynamic and economic information presented so far is summarized in Figure 46, showing a com-
parison of the ten cycles considered in terms of First and Second Law eﬃciencies and of OCC. This chart is
interesting to assess the thermal and economic performance of each cycle; for instance, the Transcritical CO2
(b), Allam (j) and Partial Cooling (f) cycles have equally low costs but, amongst them, only the Partial Cooling
system yields acceptable thermal performance. In Figure 46, thermal eﬃciency has a direct impact on the size
of the solar ﬁeld and, accordingly, the tower and receiver whilst the Carnot Factor is a measure of the overall
irreversibility of the cycle, hence the temperature gap (between the hot and cold reservoirs) needed to achieve
a given thermal eﬃciency.
Figure 46: Thermo-economic comparison of supercritical CO2cycles
As a conclusion of the foregoing thermodynamic and economic analysis, the Transcritical CO2cycle is
thought to enable installation costs lower than 6000 $/kW with almost complete certainty. Moreover, if the
85% conﬁdence interval is considered, the capital cost of this cycle decreases to about 5500 $/kW, which is
very competitive against typical values of coal power plants -3800 $/kW - or state-of-the-art CSP plants
using tower technology - 5800 $/kW -. Interestingly, this is in spite of not achieving very high thermal
eﬃciency (th <48.5%) or Carnot Factor. The Partial Cooling and the Allam layouts have moderate costs also,
in the order of 6000 $/kW respectively. For the Partial Cooling cycle, this is also accompanied by a very good
Power Block based on supercritical CO2cycles 53Power Block based on supercritical CO2cycles 53Power Block based on supercritical CO2cycles 53
thermodynamic performance, with thermal eﬃciencies higher than 50%. Finally, very complex layouts are of
no interest despite the high th.
7.5.3 Levelized Cost of Electricity
Further to the economic assessment of capital costs presented in the previous section, the associated Levelized
Cost of Electricity of the layouts of interest is presented now. This is done for the Allam and Partial Cooling
cycles, inasmuch as the Transcritical CO2cycle is very diﬃcult to implement in practice. This is because it
requires very low ambient temperatures which are not usually found in typical locations of Concentrated Solar
A good assessment of LCoE in CSP-sCO2power plants is provided in  where the general methodology
to estimate partial load conditions of the Allam and Partial Cooling power is discussed, along with the oﬀ-design
operating strategies. In this regard, three diﬀerent control strategies are compared to estimate the performance
in partial load: Inventory, By-pass and Temperature:
•Inventory: the circulating mass ﬂow rate in the system is reduced when the power demand decreases.
Carbon Dioxide is bled from the system, usually in the high pressure section, which brings about a lower
power output and, also, a general descent of pressures throughout the system. When power demand
increases, the Carbon Dioxide stored at high pressure in a vessel is reinjected back, usually in the low
pressure section to minimize pumping power.
•By-pass: this is similar to the previos one, but in this case the mass ﬂow rate is only reduced across
the high pressure and high temperature section of the power block. The turbine operates with a lower
mass ﬂow rate, hence producing less power, whilst the circulating ﬂow rat across the compressor remains
essentially the same. This control scheme is less eﬃcient than inventory but, on the other hand, it enables
fast response of the system to power output changes.
•Temperature: the circulating mass ﬂow rate remains the same so, when the heat input to the cycle
decreases, turbine inlet temperature is reduced. This is the simpler control scheme but it also brings
about a negative impact on thermal eﬃciency of the cycle.
A combination between the two ﬁrst strategies is found to obtain the best results, leading to good oﬀ-design
cycle thermal performances without detrimental eﬀects on compressor operation.
With the resulting optimum operating strategy, the analysis presented by Crespi suggests that Levelized
Costs of Electricity in the range 8.5-9.5 ¢/kWh for a good location and 9.5-11.0 ¢/kWh in a location that is
not as favourable should be expected from a CSP-sCO2power plant. Such values are slightly lower than those
achievable by a state-of-the-art CSP plant using a standard steam cycle, in particular for the Allam cycle which
seems to be able to enable a 10% reduction with respect to the latter technology. This is shown in Figure 47.
It is worth remarking that these LCoE ranges are obtained by the author for diﬀerent load dispatch modes
and boundary ﬁnancial conditions. The dispatch control model deﬁnes the operating schedule of the thermal
energy storage system and power block. For the default System Advisor Model dispatch control (System Advisor
Model SAM is a free techno-economic software model developed by the National Renewable energy Laboratory
which facilitates decision-making for people in the renewable energy industry), the turbine works at full load
whenever possible except in summer, when a 5% overload is enabled during the central hours of the day char-
acterized by the highest solar irradiation. For the SunShot Vision case, the load is reduced during winter in
order to enable longer operating hours while maintaining the rated conditions during spring and summer. The
ﬁnancial parameters in the LCoE calculation tool are also set to the values reported by these two sources, as
summarized in Table 6. The possible combinations of dispatch control and ﬁnancial models yield four cases,
shown in Table 10 for which Crespi obtains the range of Levelized Costs of Electricity presented in Figure 47.
54 Power Block based on supercritical CO2cycles54 Power Block based on supercritical CO2cycles54 Power Block based on supercritical CO2cycles
(a) Levelized Cost of Energy obtained with SAM for a CSP
located in Las Vegas.
(b) Levelized Cost of Energy obtained with SAM for a CSP
located in Tonopah.
(c) Net Present Value obtained with SAM for a CSP located in
(d) Net Present Value obtained with SAM for a CSP located in
Figure 47: LCOE and NPV obtained with SAM considering three diﬀerent cycles and four ﬁnancial/control
combinations. The locations of choice are Las Vegas and Tonopah, both in United States of America.
SAM Default SunShot Vision Study
IRR target [%] 11 15
IRR target Year 20 30
Analysis period [years] 25 35
Inﬂation rate [%] 2.5 3
Nominal Discount rate [%] 8.14 8.66
Loan Percent of total capital cost [%] 50 60
Loan Duration [years] 18 15
Loan Annual interest rate [%] 7 7.1
Table 6: Financial parameters employed in the SAM’s default and SunShot Vision cases. More information
available in .
As a complement to the results presented earlier in this section, and for the sake of clarity, a summary for the
results is presented in Figure 48, conﬁrming that Concentrated Solar Power plants using standard supercritical
Carbon Dioxide power cycles have a very narrow margin to improve the economic performance of contemporary
CSP plants based on steam turbines. This comes to conﬁrm the need to developed the SCARABEUS technology
to signiﬁcantly reduce the cost of dispatchable solar electricity.
Power Block based on supercritical CO2cycles 55Power Block based on supercritical CO2cycles 55Power Block based on supercritical CO2cycles 55
Financial Model Dispatch Control
Case 1 SAM Default SAM Default
Case 2 SAM Default SunShot Vision Study
Case 3 SunShot Vision Study SAM Default
Case 4 SunShot Vision Study SunShot Vision Study
Table 7: Diﬀerent combinations of Dispatch Control and Financial models
Figure 48: Ranges of Levelized Cost of Electricity for a number of technologies and boundary techno-economic
7.6 Projects under development worldwide
7.6.1 North America
Supercritical CO2power cycles are not commercially available yet. The largest plant based on this technology
has been developed y Net Power but this is yet a large-scale demonstration plant. This plant, located in La
Porte (TX), USA, is rated at 50 MWth (equivalent to some 25 MWe output) and has a total cost of about
150 MUSD. The power is produced from natural gas which is burned with oxygen only, hence producing water
steam and carbon dioxide in the combustion gases. The tight integration between the Air Separation Unit
(needed to produce oxygen) and the power cycle enables thermal eﬃciencies in the order of 60%.
A conceptual scheme of the Allam cycle is presented in Figure 49, along with the associated enthalpy (h)
versus pressure (p) diagram in Figure 50. The latter conﬁrms the main ﬂaw of the cycle when it comes to Con-
centrated Solar Power applications: the need to reduce the working temperature at the inlet to the compression
process to around 15oC. This pretty much prevents this cycle from being applied to hot environments as it is
mostly the case in solar thermal power plants. This was already highlighted in an earlier section.
Net Power’s demonstration plant, which does not incorporate the Air Separation unit with the aim to cut
costs down (piped ozygen is used), underwent ﬁrst ﬁring in oxycombustion mode on May 2018 and, according
to recent articles featured in specialised publications like Gas Turbine world, it is reportedly completing the
preliminary test programme . Upon successful completion of this test programme, the plans of the company
are to upscale the concept to 300 MWe which is deemed to most cost-eﬀective size for natural gas ﬁred power
plants incorporating carbon capture.
Another ﬂaship project in United States is currently being developed by The Gas Technology Institute,
General Electric and Southwest Research Institute, along with the National Renewable Energy Technology
Laboratory of the Department of Energy. This STEP (Supercritical Transformational Electric Power) pilot plant
has a budget of about 120 MUSD and it aims to deliver a ﬁrst-of-a-kind 10 MWe supercritical CO2power plant.
According to the Department of Energy (https://www.energy.gov/sco2-power-cycles/pilot-plant-supercritical-
56 Power Block based on supercritical CO2cycles56 Power Block based on supercritical CO2cycles56 Power Block based on supercritical CO2cycles
Figure 49: Layout and main speciﬁcations of the Allam cycle .
co2-power-cycles), ”this pilot project will provide valuable data on potential challenges for continuous operation
on a larger scale. Key features of the project include the following:
•Indirectly heated cycle applicable to advanced combustion boilers.
•Thermal eﬃciency ¿50% possible.
•High ﬂuid density and low pressure ratio enable compact turbomachinery.
•Ideally suited to constant temperature heat sources.
•Adaptable for dry cooling”.
The pilot plant is conceived to be able to adapt to operating on a Simple Recuperated layout and on a
Recompression layout for ﬂexibility and it is expected to be in operation by the end of 2022, according to the
schedule made public by The Gas Institute, Figure 51. The main research items are shown in Figure 52.
In addition to these demonstration projects at representative scale, the North American research facilities
listed in Table 8 are also worth noting. Even if they cannot be considered as precommercial (they are not
actually intended to be so), they have contributed to developing the technology to the current state-of-the-art.
Locationn Size Cycle Layout Institution
West-Miﬄin (PA) 100 kWeSimple Recuperated Bechtel Marine Propulsion Co.
Akkron (OH) 7.3 MWeSimple Recuperated Echogen
Albuquerque (NM) 125 kWeBrayton cycle (without turbine) SANDIA National Laboratories (New Mexico)
Albuquerque (NM) 1 MWtBrayton cycle (without turbine) SANDIA National Laboratories (New Mexico)
Arvada (CO) 20 kWeRecompression SANDIA-DOE-Barber Nichols (USA)
San Antonio (TX) 1 MWeSimple Recuperated SWRI & GE
Ottawa, Canada 50-250 kWeRecompression Carleton University (in the design phase)
San Antonio (TX) 10 MWtSimple Recuperated & Recompression STEP programme
La Porte (TX) 50 MWtAllam Net Power
Table 8: Supercritical CO2facilities currently available in United States.
Power Block based on supercritical CO2cycles 57Power Block based on supercritical CO2cycles 57Power Block based on supercritical CO2cycles 57
Figure 50: Pressure vs. enthalpy diagram of the Allam cycle .
Figure 51: Development plan of the STEP facility .
The experimental development of supercritical Carbon Dioxide technologies in Europe lags behind the activities
carried out in North America and even Asia. Despite some research projects funded by the member states and
the European Commission, the few testing facilities are of a much smaller size than the American counterparts.
The available facilities in Europe are listed in Table 9. None of them is in the megawatt scale nor is it
able to implement a complete Recompression cycle. Amongst them though, the loop currently available at the
Technical University of Vienna (TUW) will be expanded within SCARABEUS to enhance its ﬂexibility and
testing capabilities, both in terms of capacity, maximum temperature and working ﬂuid.
7.6.3 Rest of the world
Asia is, together with North America and Europe, the third largest contributor to sCO2technology development
in the world. The Tokyo Institute of Technology constructed one of the ﬁrst experimental loops to demonstrate
the Recompression cycle in the early 2000s, Figure 53 but this was at a very small scale (target output was
58 Power Block based on supercritical CO2cycles58 Power Block based on supercritical CO2cycles58 Power Block based on supercritical CO2cycles
Figure 52: Foreseen conﬁgurations in the STEP facility .
Site of Construction Size Power Cycle Institution
Husinec-Rez, Czech Republic 0.35 kg/s Recompression (without turbine) Research Center Rez (Czech Republic)
Stuttgart, Germany not declared Brayton cycle (only heat exchangers) sCO2Hero Project partners
Wien, Austria 0.35 kg/s Simle Recuperated TU Wien
Table 9: Supercritical CO2facilities currently available in Europe.
below 10 kWe) and the activity was interrupted soon after [135, 136].
The development of sCO2technologies has been more active in South Korea in recent years. Aimed at
nuclear application initially and with a focus on coal later, several National Research Institutes like The Korea
Advance Institute of Science and Technology KAIST, Korea Atomic Energy Reseach Institute KAERI and the
Korea Institute of Energy Research KIER have been actively developing experimental small-scale loops to test
diﬀerent cycle layouts and demonstrate cycle performance [137, 138]. More recently, the Gas Technology Insti-
tute (USA), the Korean Electric Power Reseasch Institute KEPRI, and the Korean Electric Power Company
KEPCO, national utility, have signed a Memorandum of Understanding to develop supercritical CO2power
cycle technologies that could impact power generation eﬀorts. This MoU enables the active involvement of
KEPCO in the aforecite STEP plant.
Other facilities available worlwide are
Site of Construction Size Power Cycle Institution
Daejeon, South Korea 10 kWeBrayton Cylce KIER (South Korea)
Daejeon, South Korea 80 kWeDual Simple Recuperated Cylce KIER (South Korea)
Daejeon, South Korea 1 kWeRecuperated Cylce KIER (South Korea)
Daejeon, South Korea kW-scale Recuperated Cylce KAIST (South Korea)
Tokyo, Japan 10 kWeSimple Recuperated Tokyo Institute of Technology (Japan)
Table 10: Supercritical CO2facilities currently available in Asia.
Power Block based on supercritical CO2cycles 59Power Block based on supercritical CO2cycles 59Power Block based on supercritical CO2cycles 59
Figure 53: Layout of the experimental loop at Tokyo Institute of Technology .
Figure 54: Layout of the experimental loop at Korea Advance Institute of Science and Technology .
Figure 55: Layout of the experimental loop at Korea Institute of Energy Research .
In addition to the experimental activities cited in this section, there are other initiatives planned or un-
der development in other regions of the world like Australia or India. They all contribute to the development
of the technology, even if they are not listed in this section due to their somewhat smaller impact internationally.
60 Conclusions60 Conclusions60 Conclusions
This report assessing the current state of the art provides an overview of the technology used in Concen-
trated Solar Power plants based on central receiver technology (tower). The main subsystems of a power plant
incorporating Thermal Energy Storage are discussed as so are the foreseen development trends.
The potential of conventional supercritical Carbon Dioxide power cycles to supersede steam turbines has
also been explored in the report. An assessment of the layouts with larger potential for Concentrated Solar
Power applications along with discussions about their thermodynamic and economic potential allows for a rea-
soned comparison between this technology and the steam technology used by default in commercial power plants.
Overall, based on data and forecasts issued by the International Renewable Energy Agency IRENA, it is
concluded that the current cost of electricity produced by Concentrated Solar Power plants is in the order
of 8-15 ¢/kWh, though these values are very site-speciﬁc and they can increase in certain sites with speciﬁc
boundary conditions. This cost is not expected to drop substantially in the short term as this would only be
enabled by a similar increase of thermal eﬃciency, and only a slight reduction seems possible if economies of
scale are implemented.
On the other hand, supercritical CO2technologies do have the potential to enable lower costs, mostly thanks
to the higher eﬃciency of the power block (bringing about a reduction of the solar ﬁeld size) and the smaller
footprint, therefore cost, of this part of the plant. According to the analyses available in literature, levelized
costs of electricity of conventional supercritical CO2based CSP are expected to be in the order of 9.5-10 ¢/kWh
in favourable conditions. Nevertheless, these ﬁgures are very conservative and incorporate a large safety margin
to account for uncertainty which means that the actual LCoE is likely to be substantially lower than these
values. Indeed, the potential of sCO2-CSP to enable lower costs of electricity than conventional CSP is widely
acknowledged; unfortunately, the usual boundary conditions found in typical CSP sites prevent the implemen-
tation of the most eﬃcient supercritical CO2layouts, what brings about an inevitable rise of the electricity costs
achievable by this innovative power block technology. Therefore, for warm environments, the levelized cost of
electricity of CSP-sCO2plants is expected to be not signiﬁcantly lower than that of conventional CSP.
In the light of these results, it becomes clear that in order to exploit the full potential of supecritical CO2
technology, it is mandatory to enable the implementation of the most eﬃcient sCO2cycle layouts, which is the
main driver of SCARABEUS. This key enabling project is thus supported on the need to implement condensing
cycles whose performance, as discussed in this report, clearly exceeds that of conventional steam power plants.
By doing so, the cost reduction brought about by sCO2power blocks will be larger than the possible uncertainty
inherent to the calculations of thermal performance and costs of this new generation of power plants, therefore
ensuring the economic and technical advantage of CSP-sCO2over conventional CSP.
References 61References 61References 61
 IEA (International Energy Agency). World Energy Outlook Special Report 2018: Energy and Climate
change - executive summary.
 WRI (World Resource Institute). climate analysis indicators tool (CAIT) 2.0: WRI’s climate data ex-
plorer, 2014, accessed September 2019.
 FAO (Food and Agriculture Organization). FAOSTAT: Emissions - land use, 2014, accessed November
 IPCC (Intergovernental Panel on Climate Change). mitigation of climate change: Trends in stocks and
ﬂows of GHGs and their drivers, 2014, accessed November 2018.
URL https://www.ipcc.ch/pdf/unfccc/sbsta40/SED/1 blanco sed3.pdf
 L. F. Cabeza, E. Galindo, C. Prieto, C. Barreneche, A. I. Fern´andez, Key performance indica-
tors in thermal energy storage: Survey and assessment, Renewable Energy 83 (2015) 820 – 827.
 A. Gil, M. Medrano, I. Martorell, A. L´azaro, P. Dolado, B. Zalba, L. F. Cabeza, State of
the art on high temperature thermal energy storage for power generation. part 1—concepts, ma-
terials and modellization, Renewable and Sustainable Energy Reviews 14 (1) (2010) 31 – 55.
 S. J. Wagner, E. S. Rubin, Economic implications of thermal energy storage for concentrated solar thermal
power, Renewable Energy 61 (2014) 81 – 95, world Renewable Energy Congress – Sweden, 8–13 May, 2011,
Link¨oping, Sweden. doi:https://doi.org/10.1016/j.renene.2012.08.013.
 J. Hern´andez-Moro, J. Mart´ınez-Duart, CSP electricity cost evolution and grid parities based on the
IEA roadmaps, Energy Policy 41 (2012) 184 – 192, modeling Transport (Energy) Demand and Policies.
 E. Gonz´alez-Roubaud, D. P´erez-Osorio, C. Prieto, Review of commercial thermal energy storage in con-
centrated solar power plants: Steam vs. molten salts, Renewable and sustainable energy reviews 80 (2017)
 U. Herrmann, D. W. Kearney, Survey of thermal energy storage for parabolic trough power plants, Journal
of solar energy engineering 124 (2) (2002) 145–152.
 O. Behar, A. Khellaf, K. Mohammedi, S. Ait-Kaci, A review of integrated solar combined cycle system
(ISCCS) with a parabolic trough technology, Renewable and Sustainable Energy Reviews 39 (2014) 223–
 Solar Paces website CSP technology description, visited September 2019.
 Linear concentrator system basics for concentrating solar power, visited September 2019.
concentrating-solar-power? sm au =i5VJs1P6vNVRTjT7
 C. J. Noone, M. Torrilhon, A. Mitsos, Heliostat ﬁeld optimization: A new computa-
tionally eﬃcient model and biomimetic layout, Solar Energy 86 (2) (2012) 792 – 803.
62 References62 References62 References
 A. Poullikkas, G. Kourtis, I. Hadjipaschalis, Parametric analysis for the installation of solar dish tech-
nologies in mediterranean regions, Renewable and Sustainable Energy Reviews 14 (9) (2010) 2772 – 2783.
 F. T´ellez, M. Burisch, C. Villasante, M. S´anchez, C. Sansom, P. Kirby, C. Caliot, A. Ferriere,
C. A. Bonanos, C. Papanicolas, A. Montenon, R. Monterreal, J. Fern´andez, State of the Art in He-
liostats and Deﬁnition of Speciﬁcations (Survey for a low cost heliostat development) (Jul. 2017).
 F. Arbes, G. Weinrebe, M. W¨ohrbach, Heliostat ﬁeld cost reduction by ‘slope drive’ optimization, AIP
Conference Proceedings 1734 (1) (2016) 160002. doi:10.1063/1.4949243.
 Visited September 2019. [link].
 W. B. Stine, M. Geyer, Power From The Sun by William B. Stine and Michael Geyer, 2001.
 F. J. Collado, J. Guallar, A review of optimized design layouts for solar power tower
plants with campo code, Renewable and Sustainable Energy Reviews 20 (2013) 142 – 154.
 J. Wang, L. Duan, Y. Yang, An improvement crossover operation method in ge-
netic algorithm and spatial optimization of heliostat ﬁeld, Energy 155 (2018) 15 – 28.
 S. Kiwan, A. L. Khammash, Investigations into the spiral distribution of the heliostat ﬁeld in solar central
tower system, Solar Energy 164 (2018) 25 – 37. doi:https://doi.org/10.1016/j.solener.2018.02.042.
 M. Zhang, L. Yang, C. Xu, X. Du, An eﬃcient code to optimize the heliostat ﬁeld and compar-
isons between the biomimetic spiral and staggered layout, Renewable Energy 87 (2016) 720 – 730.
 M. Zhang, X. Du, L. Yang, C. Xu, Y. Yang, Comparing study of biomimetic spiral and ra-
dial staggered layouts of the heliostat ﬁeld, Energy Procedia 69 (2015) 242 – 249, interna-
tional Conference on Concentrating Solar Power and Chemical Energy Systems, SolarPACES 2014.
 Y. Yao, Y. Hu, S. Gao, Heliostat ﬁeld layout methodology in central receiver systems based on eﬃciency-
related distribution, Solar Energy 117 (2015) 114 – 124. doi:https://doi.org/10.1016/j.solener.2015.04.029.
 S. Kim, I. Lee, B. J. Lee, Development of performance analysis model for central receiver system
and its application to pattern-free heliostat layout optimization, Solar Energy 153 (2017) 499 – 507.
 E. Scouros, A. Cosmetatos, Placement of heliostats on an uneven landscape, Energy Pro-
cedia 49 (2014) 220 – 228, proceedings of the SolarPACES 2013 International Conference.
 N. Cruz, S. Salhi, J. Redondo, J. ´alvarez, M. Berenguel, P. Ortigosa, Hector, a new methodology
for continuous and pattern-free heliostat ﬁeld optimization, Applied Energy 225 (2018) 1123 – 1131.
 E. Carrizosa, C. Dom´ınguez-Bravo, E. Fern´andez-Cara, M. Quero, An optimization approach to the design
of multi-size heliostat ﬁelds, 2014.
References 63References 63References 63
 R. Perez-Enciso, A. Gallo, D. Riveros-Rosas, E. Fuentealba-Vidal, C. Perez-R´abago, A simple method to
achieve a uniform ﬂux distribution in a multi-faceted point focus concentrator, Renewable Energy 93 (C)
(2016) 115–124. doi:10.1016/j.renene.2016.02.
 N. Cruz, J. ´alvarez, J. Redondo, M. Berenguel, P. Ortigosa, A two-layered solution for auto-
matic heliostat aiming, Engineering Applications of Artiﬁcial Intelligence 72 (2018) 253 – 266.
 A. S´anchez-Gonz´alez, M. R. Rodr´ıguez-S´anchez, D. Santana, Aiming strategy model based on al-
lowable ﬂux densities for molten salt central receivers, Solar Energy 157 (2017) 1130 – 1144.
 A. Salom´e, F. Chhel, G. Flamant, A. Ferri`ere, F. Thiery, Control of the ﬂux distribution on a solar tower
receiver using an optimized aiming point strategy: Application to themis solar tower, Solar Energy 94
(2013) 352 – 366. doi:https://doi.org/10.1016/j.solener.2013.02.025.
 H. Benoit, L. Spreaﬁco, D. Gauthier, G. Flamant, Review of heat transfer ﬂuids in tube-receivers used in
concentrating solar thermal systems: Properties and heat transfer coeﬃcients, Renewable and Sustainable
Energy Reviews 55 (2016) 298 – 315. doi:https://doi.org/10.1016/j.rser.2015.10.059.
 P. K. Falcone, A handbook for solar central receiver design, Tech. rep., Sandia National Labs., Livermore,
CA (USA) (1986).
 W. Apley, Systems analysis of solar thermal power systems. report on task 1: determination and charac-
terization of solar thermal conversion options, Tech. rep., Battelle Paciﬁc Northwest Labs., Richland, WA
 M. Haeger, A. Valverde, W. Meinecke, S. Cordes, Phoebus technology program solar air receiver (TSA)
operational experience and test evaluation of the 2.5 mw (th) volumetric air receiver test facility at the
plataforma solar de almeria, 1994.
 J. Spelling, Hybrid solar gas-turbine power plants: a thermoeconomic analysis, Ph.D. thesis, KTH Royal
Institute of Technology (2013).
 M. Quero, R. Korzynietz, M. Ebert, A. Jim´enez, A. Del R´ıo, J. Brioso, Solugas–operation experience of the
ﬁrst solar hybrid gas turbine system at mw scale, Energy Procedia 49 (Supplement C) (2014) 1820–1830.
 R. Korzynietz, J. Brioso, A. Del R´ıo, M. Quero, M. Gallas, R. Uhlig, M. Ebert, R. Buck, D. Teraji,
Solugas–comprehensive analysis of the solar hybrid brayton plant, Solar Energy 135 (2016) 578–589.
 G. Flamant, D. Gauthier, H. Benoit, J.-L. Sans, B. Boissi`ere, R. Ansart, M. Hemati, A new heat transfer
ﬂuid for concentrating solar systems: Particle ﬂow in tubes, Energy Procedia 49 (2014) 617–626.
 P. Falcone, J. Noring, J. Hruby, Assessment of a solid particle receiver for a high temperature solar central
receiver system, Tech. rep., Sandia National Labs., Livermore, CA (USA) (1985).
 L. Radosevich, A. Skinrood, The power production operation of solar one, the 10 mwe solar thermal
central receiver pilot plant, Journal of solar energy engineering 111 (2) (1989) 144–151.
 B. Kelly, M. Singh, Summary of the ﬁnal design for the 10 mwe solar two central receiver project, Tech.
rep., American Society of Mechanical Engineers, New York, NY (United States) (1995).
 M. S´anchez, Advanced molten salt receiver RAS (in spanish), Tech. rep., Ciemat (1998).
 R. Fern´andez, Recevier technology: Short course on concentrating solar systems (in spanish), Tech. rep.,
64 References64 References64 References
 D. Bellard, A. Ferriere, F. Pra, R. Couturier, Experimental characterization of a high-temperature pres-
surized air solar absorber for the pegase project, in: Proceedings of the 18th SolarPACES Conference,
Marrakech, Morocco, 2012.
 E. S. Freeman, The kinetics of the thermal decomposition of sodium nitrate and of the reaction between
sodium nitrite and oxygen, The Journal of Physical Chemistry 60 (11) (1956) 1487–1493.
 K. Stahl, J. Griﬃn, B. Matson, R. Pettit, Optical characterization of solid particle solar central receiver
materials, Tech. rep., Paciﬁc Northwest Lab., Richland, WA (USA) (1986).
 N. P. Siegel, C. K. Ho, S. S. Khalsa, G. J. Kolb, Development and evaluation of a prototype solid particle
receiver: on-sun testing and model validation, Journal of solar energy engineering 132 (2) (2010) 021008.
 H. Chen, Y. Chen, H.-T. Hsieh, N. Siegel, Computational ﬂuid dynamics modeling of gas-particle ﬂow
within a solid-particle solar receiver, Journal of solar energy engineering 129 (2) (2007) 160–170.
 K. Kim, N. Siegel, G. Kolb, V. Rangaswamy, S. F. Moujaes, A study of solid particle ﬂow characterization
in solar particle receiver, Solar Energy 83 (10) (2009) 1784–1793.
 T. Tan, Y. Chen, Z. Chen, N. Siegel, G. J. Kolb, Wind eﬀect on the performance of solid particle solar
receivers with and without the protection of an aerowindow, Solar Energy 83 (10) (2009) 1815–1827.
 T. Tan, Y. Chen, Review of study on solid particle solar receivers, Renewable and Sustainable Energy
Reviews 14 (1) (2010) 265–276.
 K. M. Armijo, C. Ho, R. Anderson, J. Christian, S. Babiniec, J. Ortega, Magnetic ﬁeld ﬂow phenomena
in a falling particle receiver, in: AIP Conference Proceedings, Vol. 1734, AIP Publishing, 2016, p. 030004.
 L. Amsbeck, R. Buck, T. Prosin, Particle tower technology applied to metallurgic plants and peak-time
boosting of steam power plants, in: AIP Conference Proceedings, Vol. 1734, AIP Publishing, 2016, p.
 J. Christian, C. Ho, Design requirements, challenges, and solutions for high-temperature falling particle
receivers, in: AIP Conference Proceedings, Vol. 1734, AIP Publishing, 2016, p. 030008.
 C. K. Ho, J. M. Christian, J. Yellowhair, N. Siegel, S. Jeter, M. Golob, S. I. Abdel-Khalik, C. Nguyen,
H. Al-Ansary, On-sun testing of an advanced falling particle receiver system, in: AIP Conference Pro-
ceedings, Vol. 1734, AIP Publishing, 2016, p. 030022.
 H. Ibrahim, A. Ilinca, Techno-economic analysis of diﬀerent energy storage technologies, in: Energy
Storage-Technologies and Applications, IntechOpen, 2013.
 IRENA (International Renewable Energy Agency). renewable energy technologies: Cost analysis series,
power Sector Issue 2/5 Concentrating Solar Power (2012).
 H. Zhao, Q. Wu, S. Hu, H. Xu, C. N. Rasmussen, Review of energy storage system for wind power
integration support, Applied energy 137 (2015) 545–553.
 D. Akinyele, R. Rayudu, Review of energy storage technologies for sustainable power networks, Sustainable
Energy Technologies and Assessments 8 (2014) 74–91.
 X. Luo, J. Wang, M. Dooner, J. Clarke, Overview of current development in electrical energy storage
technologies and the application potential in power system operation, Applied energy 137 (2015) 511–536.
 K. Divya, J. Østergaard, Battery energy storage technology for power systems—an overview, Electric
power systems research 79 (4) (2009) 511–520.
References 65References 65References 65
 P. K. Choubey, M.-s. Kim, R. R. Srivastava, J.-c. Lee, J.-Y. Lee, Advance review on the exploitation
of the prominent energy-storage element: Lithium. part i: From mineral and brine resources, Minerals
Engineering 89 (2016) 119–137.
 S. Kuravi, J. Trahan, D. Y. Goswami, M. M. Rahman, E. K. Stefanakos, Thermal energy storage tech-
nologies and systems for concentrating solar power plants, Progress in Energy and Combustion Science
39 (4) (2013) 285–319.
 U.S. department of energy. 2014 sunshot initiative portfolio book: concentrating solar power. washington,
dc: Oﬃce of energy eﬃciency & renewable energy, U.S. department of energy; 2014.
 R. Sioshansi, P. Denholm, The value of concentrating solar power and thermal energy storage, IEEE
Transactions on Sustainable Energy 1 (3) (2010) 173–183.
 H. E. Reilly, G. J. Kolb, An evaluation of molten-salt power towers including results of the solar two
project; topical, Tech. rep., Sandia National Labs. (2001).
 U. Herrmann, M. Geyer, D. Kearney, Overview on thermal storage systems; workshop on thermal storage
for trough power systems (2006).
 W. Goldstern, Steam storage installations: Construction, design and operation of industrial heat accu-
mulators, Oxford: Pergamon Press, 1970.
 W.-D. Steinmann, M. Eck, Buﬀer storage for direct steam generation, Solar Energy 80 (10) (2006) 1277–
 M. Geyer, Solar Power Plants. Chapter 6: Thermal storage for solar power plants, Springer-Verlag Berlin
Heidelberg, 1991. doi:https://doi.org/10.1007/978-3-642-61245-9 6.
 J. Avellaner, C. Ortiz, F. Martinez, F. Sanchez, Cesa-1 project status report, in: Thermo-Mechanical
Solar Power Plants, Springer, 1985, pp. 73–82.
 J. Andujar, F. Rosa, M. Geyer, Cesa-1 thermal storage system evaluation, Solar Energy 46 (5) (1991)
 J. Bezian, B. Bonduelle, B. Rivoire, Prospective evaluation of molten salt solar plants based on themis
results, in: Advances In Solar Energy Technology, Elsevier, 1988, pp. 1666–1670.
 G. J. Kolb, An evaluation of possible next-generation high-temperature molten-salt power towers, Sandia
National Laboratories, Albuquerque, NM, Report No. SAND2011-9320 122 (2011) 149.
 S. Guillot, A. Faik, A. Rakhmatullin, J. Lambert, E. Veron, P. Echegut, C. Bessada, N. Calvet, X. Py,
Corrosion eﬀects between molten salts and thermal storage material for concentrated solar power plants,
Applied Energy 94 (2012) 174–181.
 M. Liu, W. Saman, F. Bruno, Review on storage materials and thermal performance enhancement tech-
niques for high temperature phase change thermal storage systems, Renewable and Sustainable Energy
Reviews 16 (4) (2012) 2118–2132.
 A. Maccari, D. Bissi, G. Casubolo, F. Guerrini, L. Lucatello, G. Luna, A. Rivaben, E. Savoldi, S. Tamano,
M. Zuanella, Archimede solar energy molten salt parabolic trough demo plant: a step ahead towards the
new frontiers of csp, Energy Procedia 69 (2015) 1643–1651.
 C. Prieto, R. Osuna, A. I. Fern´andez, L. F. Cabeza, Thermal storage in a mw scale. molten salt solar
thermal pilot facility: Plant description and commissioning experiences, Renewable energy 99 (2016)
66 References66 References66 References
 G. Peir´o, J. Gasia, L. Mir´o, C. Prieto, L. F. Cabeza, Experimental analysis of charging and discharging
processes, with parallel and counter ﬂow arrangements, in a molten salts high temperature pilot plant
scale setup, Applied energy 178 (2016) 394–403.
 C. Prieto, L. Mir´o, G. Peir´o, E. Or´o, A. Gil, L. F. Cabeza, Temperature distribution and heat losses in
molten salts tanks for csp plants, Solar Energy 135 (2016) 518–526.
 M. Medrano, A. Gil, I. Martorell, X. Potau, L. F. Cabeza, State of the art on high-temperature thermal
energy storage for power generation. part 2—case studies, Renewable and Sustainable Energy Reviews
14 (1) (2010) 56–72.
 J. E. Pacheco, R. W. Bradshaw, D. B. Dawson, W. De la Rosa, R. Gilbert, S. H. Goods, M. J. Hale,
P. Jacobs, S. A. Jones, G. J. Kolb, et al., Final test and evaluation results from the solar two project,
Report No. SAND2002-0120, Sandia National Laboratories, Albuquerque, NM 45.
 J. E. Pacheco, R. Gilbert, Overview of recent results of the solar two test and evaluations program, Tech.
rep., Sandia National Labs., Albuquerque, NM (US) (1999).
 M. Liu, N. S. Tay, S. Bell, M. Belusko, R. Jacob, G. Will, W. Saman, F. Bruno, Review on concentrat-
ing solar power plants and new developments in high temperature thermal energy storage technologies,
Renewable and Sustainable Energy Reviews 53 (2016) 1411–1432.
 F. J. Ruiz-Caba˜nas, C. Prieto, R. Osuna, V. Madina, A. I. Fern´andez, L. F. Cabeza, Corrosion testing
device for in-situ corrosion characterization in operational molten salts storage tanks: A516 gr70 carbon
steel performance under molten salts exposure, Solar Energy Materials and Solar Cells 157 (2016) 383–392.
 K. Federsel, J. Wortmann, M. Ladenberger, High-temperature and corrosion behavior of nitrate nitrite
molten salt mixtures regarding their application in concentrating solar power plants, Energy Procedia 69
 J. E. Pacheco, H. E. Reilly, G. J. Kolb, C. E. Tyner, Summary of the solar two test and evaluation
program, Tech. rep., Sandia National Labs., Albuquerque, NM (US); Sandia National Labs . .. (2000).
 R. W. Bradshaw, W. M. Clift, Eﬀect of chloride content of molten nitrate salt on corrosion of a516 carbon
steel, Sandia report.
 K. Vignarooban, X. Xu, A. Arvay, K. Hsu, A. M. Kannan, Heat transfer ﬂuids for concentrating solar
power systems–a review, Applied Energy 146 (2015) 383–396.
 G. Garc´ıa-Mart´ın, M. Lasanta, V. Encinas-S´anchez, M. De Miguel, F. P´erez, Evaluation of corrosion
resistance of a516 steel in a molten nitrate salt mixture using a pilot plant facility for application in csp
plants, Solar Energy Materials and Solar Cells 161 (2017) 226–231.
 D. M. Blake, L. Moens, M. J. Hale, H. Price, D. Kearney, U. Herrmann, New heat transfer and storage
ﬂuids for parabolic trough solar thermal electric plants, in: Proceedings of the 11th SolarPACES Interna-
tional Symposium On concentrating Solar Power and Chemical Energy Technologies. Zurich, Switzerland,
 M. M. Kenisarin, High-temperature phase change materials for thermal energy storage, Renewable and
Sustainable energy reviews 14 (3) (2010) 955–970.
 Coastal Chemical Co, HITEC heat transfer salt. information provided by coastal chemical.
 Badger Energy Corp, Design, handling, operation and maintenance procedures for hitec molten salt,
SAND 81-8179 (1981).
 U. Herrmann, B. Kelly, H. Price, Two-tank molten salt storage for parabolic trough solar power plants,
Energy 29 (5-6) (2004) 883–893.
References 67References 67References 67
 G. J. Kolb, R. B. Diver, Conceptual design of an advanced trough utilizing a molten salt working ﬂuid.,
Tech. rep., Sandia National Lab.(SNL-NM), Albuquerque, NM (United States) (2008).
 J. W. Raade, D. Padowitz, Development of molten salt heat transfer ﬂuid with low melting point and
high thermal stability, Journal of Solar Energy Engineering 133 (3) (2011) 031013.
 G. J. Janz, Physical properties data compilations relevant to energy storage. parts i, ii and iv, Tech. rep.,
NATIONAL STANDARD REFERENCE DATA SYSTEM, nSRDS-NBS 61 (1981).
 R. W. Bradshaw, N. P. Siegel, Development of molten nitrate salt mixtures for concentrating solar power
systems, SolarPACES, Berlin.
 C.-J. Li, P. Li, K. Wang, E. E. Molina, Survey of properties of key single and mixture halide salts
for potential application as high temperature heat transfer ﬂuids for concentrated solar thermal power
systems, AIMS Energy 2 (2) (2014) 133–157.
 A. Leyzerovich, Steam Turbines for Modern Fossil-Fuel Power Plants, The Fairmont Press, 2007.
 R. Haywood, Analysis of Engineering Cycles, Pergamon Press, 1998.
 NREL database, 29/11/2019, https://solarpaces.nrel.gov.
 IRENA, Renewable Power Generations Costs in 2018.
 U. EIA, Annual energy outlook 2015: with projections to 2040.
 M. Mehos, C. Turchi, J. Vidal, M. Wagner, Z. Ma, C. Ho, W. Kolb, C. Andraka, A. Kruizenga, Concen-
trating solar power Gen3 demonstration roadmap, Tech. rep., National Renewable Energy Lab.(NREL),
Golden, CO (United States) (2017).
 G. Angelino, Carbon Dioxide Condensation Cycles for Power Production, Journal of Engineering for
Power 90 (3) (1968) 287–295.
 E. Feher, The Supercritical Thermodynamic Power Cycle, Energy Conversion and Management 8 (1968)
 F. Crespi, G. Gavagnin, D. S´anchez, G. S. Mart´ınez, Supercritical carbon dioxide cycles for power gener-
ation: A review, Applied Energy 195 (2017) 152–183.
 V. Dostal, M. Driscoll, P. Hejzlar, A supercritical carbon dioxide cycle for next generation nuclear reactors,
Ph.D. thesis, Massachusetts Institute of Technology (2004).
 G. Angelino, Real Gas Eﬀects in Carbon Dioxide Cycles., in: ASME 1969 Gas Turbine Conference and
Products Show, Cleveland,OH, 1969.
 R. Allam, J. Fetvedt, B. Forrest, D. Freed, The Oxy-Fuel, Supercritical CO2Allam Cycle: New Cycle
Developments to Produce Even Lower-Cost Electricity From Fossil Fuels Without Atmospheric Emis-
sions, in: ASME Turbo Expo 2014: Turbine Technical Conference and Exposition, American Society of
Mechanical Engineers, Dusseldorf, 2014.
 G. Klemenic, S. Flegkas, A. Werner, M. Haider, H. Leibinger, Comparison of conventional and CO2power
generation cycles for waste heat recovery, in: The 5th Supercritical CO2Power Cycles Symposium, San
Antonio, TX, 2016, pp. 1–15.
 Y. Chen, P. Lundqvist, A. Johansson, P. Platell, A comparative study of the carbon dioxide transcritical
power cycle compared with an organic Rankine cycle with R123 as working ﬂuid in waste heat recovery,
Applied Thermal Engineering 26 (17) (2006) 2142–2147.
68 References68 References68 References
 E. Cayer, N. Galanis, M. Desilets, H. Nesreddine, P. Roy, Analysis of a carbon dioxide transcritical power
cycle using a low temperature source, Applied Energy 86 (7) (2009) 1055–1063.
 Y. Song, J. Wang, Y. Dai, E. Zhou, Thermodynamic analysis of a transcritical CO2power cycle driven
by solar energy with liquiﬁed natural gas as its heat sink, Applied energy 92 (2012) 194–203.
 R. V. Padilla, Y. C. S. Too, R. Benito, R. McNaughton, W. Stein, Thermodynamic feasibility of alternative
supercritical CO2Brayton cycles integrated with an ejector, Applied Energy 169 (2016) 49–62.
 F. Crespi, G. Gavagnin, D. S´anchez, G. S. Mart´ınez, Analysis of the Thermodynamic Potential of Super-
critical Carbon Dioxide Cycles: A Systematic Approach, Journal of Engineering for Gas Turbines and
Power 140 (2017) 051701.
 Y. Ahn, J. I. Lee, Study of various Brayton cycle designs for small modular sodium-cooled fast reactor,
Nuclear Engineering and Design 276 (2014) 128–141.
 G. Silvestri, Eddystone Station, 325 MW Generating Unit, A Brief History (2003).
 A. Armor, Ultrasupercritical Steam Turbines: Design and Materials Issues for the Next Generation (2002).
 F. Crespi, D. S´anchez, J. M. Rodr´ıguez, G. Gavagnin, A thermo-economic methodology to select sco2
power cycles for csp applications, Renewable Energy.
 F. Crespi, D. S´anchez, T. S´anchez, G. S. Mart´ınez, Capital Cost Assessment of Concentrated Solar Power
Plants Based on Supercritical Carbon Dioxide Power Cycles, Journal of Engineering for Gas Turbines and
Power 141 (2019) 071011.
 F. Crespi, D. S´anchez, T. S´anchez, G. S. Mart´ınez, Integral techno-economic analysis of supercritical car-
bon dioxide cycles for concentrated solar power, in: ASME Turbo Expo 2018: Turbomachinery Technical
Conference and Exposition, American Society of Mechanical Engineers Digital Collection, 2018.
 A. Daabo, S. Mahmoud, R. Al-Dadah, The optical eﬃciency of three diﬀerent geometries of a small scale
cavity receiver for concentrated solar applications, Applied Energy 179 (2016) 1081–1096.
 Various, Cost and Performance Data for Power Generation Technologies, Tech. rep., Black & Veatch for
the National Renewable Energy Laboratory, Cambridge, MA (2012).
 Various, The Power to Change: Solar and Wind Cost Reduction Potential to 2025, Tech. rep., IRENA,
Abu Dhabi, United Arab Emirates (2016).
 F. Crespi, Thermo-Economic Assessment of Supercritical co2Power Cycles for Concentrated Solar Power
Plants, Ph.D. thesis, University of Seville (2020).
 D. Flin, First Fire for La Porte Carbon Demo, Gas Turbine World.
 R. Allam, Carbon Capture & Utilisation from Power Generation, in: Proceedings of NEPIC International
Bioresources Conferences, North East of England Process Industry Cluster, Newcastle, UK, 2014.
 V. Bush, GTI STEP forward on sCO2Power, in: The 6th Supercritical CO2Power Cycles Symposium,
Pittsburgh, PA, 2018, pp. 1–24.
 M. Utamura, H. Hasuike, T. Yamamoto, Demonstration Test Plan of Closed Cycle Gas Turbine with
Super-Critical CO2as Working Fluid, in: 5th Conference on Sustainable Development of Energy Water
and Environment Systems, Dubrovnik, 2009, pp. 459–465.
 M. Utamura, H. Hasuike, K. Ogawa, T. Yamamoto, T. Fukushima, T. Watanabe, T. Himeno, Demon-
stration of Supercritical CO2Closed Regenerative Cycle in a Bench Scale Eexperiment, in: ASME Turbo
Expo 2012: Turbine Technical Conference and Exposition, American Society of Mechanical Engineers,
References 69References 69References 69
 J. Ik Lee, Activities at the Korea Institute of Science and Technology, in: The 5th Supercritical CO2
Power Cycles Symposium, San Antonio, TX, 2016.
 J. Cho, H. Shin, H.-S. Ra, G. Lee, C. Roh, B. Lee, Y.-j. Baik, Development of the Supercritical Carbon
Dioxide Power Cycle Experimental Loop in KIER, in: ASME (Ed.), Proceeding of ASME Turbo Expo
2016: Turbomachinery Technical Conference and Exposition, Seoul, 2016.