*Article* **System Performance Analyses of Supercritical CO<sup>2</sup> Brayton Cycle for Sodium-Cooled Fast Reactor**

**Min Xie <sup>1</sup> , Jian Cheng <sup>2</sup> , Xiaohan Ren 3,\* , Shuo Wang <sup>4</sup> , Pengcheng Che <sup>1</sup> and Chunwei Zhang <sup>1</sup>**

	- Institute of Thermal Science and Technology, Shandong University, Jinan 250061, China

3

**Abstract:** The system performance of the supercritical CO<sup>2</sup> Brayton cycle for the Sodium Fast Reactor with a partial-cooling layout was studied, and an economic analysis was carried out. The energetic, exergetic, and exergoeconomic analyses are presented, and the optimized results were compared with the recompression cycle. The sensitivity analyses were conducted by considering the variations in the pressure ratios and inlet temperatures of the main compressor and the turbine. The exergy efficiency of the partial-cooling cycle reached 63.65% with a net power output of 34.39 MW via optimization. The partial-cooling cycle obtained a minimum total cost rate of 2230.36 USD/h and exergy efficiency of 63.65% when the pressure ratio was equal to 3.50. The inlet temperature of the main compressor was equal to 35 ◦C, and the inlet temperature of the turbine was equal to 480 ◦C. The total cost of recuperators decreased with the increase in the pressure ratio and the inlet temperatures of the main compressor. In addition, the total cost of recuperator could be reduced by increasing the outlet temperature of the turbine. The change in cost from exergy loss and destruction with the pressure ratio was substantially larger than with the inlet temperature of the turbine or the main compressor. Manipulating the pressure ratio is an essential method to guarantee good economy of the system. Moreover, capital investment, operation, and maintenance costs normally accounted for large proportions of the total cost rate, being almost double the cost from the exergy loss and destruction occurring in each condition.

**Keywords:** partial-cooling cycle; supercritical CO<sup>2</sup> Brayton cycle; advanced fast reactors; exergoeconomic analyses; CO<sup>2</sup> utilization

### **1. Introduction**

The supercritical CO<sup>2</sup> (sCO2) cycle was proposed in a patent that used CO<sup>2</sup> as the working fluid [1] in 1968, but this cycle slowly developed due to the technology limitation at that time. The sCO<sup>2</sup> cycle is currently regarded as having the potential to work effectively with multiple heat sources. The first known business unit of the CO<sup>2</sup> cycle is EPS-100, and many studies on the waste heat recovery have also been conducted [2,3]. Numerous countries have also launched different scales of experimental projects. The R&D of sCO<sup>2</sup> Brayton technology is generally divided into several phases from the system design to the pilot station operation. In addition to EPS-100, the SunShot Program in the USA, the Hero-sCO<sup>2</sup> Program and the flex-sCO<sup>2</sup> Project in the European Union, and the 5-MWe sCO<sup>2</sup> pilot station in China are available. The application of the sCO<sup>2</sup> Brayton cycle has advantages of a high energy density, compactness, and high efficiency due to the good thermophysical properties of sCO<sup>2</sup> [4]. In addition to pure CO2, using a CO2-based binary mixture may be used for raising the critical temperature [5,6].

**Citation:** Xie, M.; Cheng, J.; Ren, X.; Wang, S.; Che, P.; Zhang, C. System Performance Analyses of Supercritical CO<sup>2</sup> Brayton Cycle for Sodium-Cooled Fast Reactor. *Energies* **2022**, *15*, 3555. https://doi.org/ 10.3390/en15103555

Academic Editor: Francesco Frusteri

Received: 17 March 2022 Accepted: 28 April 2022 Published: 12 May 2022

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**Copyright:** © 2022 by the authors. Licensee MDPI, Basel, Switzerland. This article is an open access article distributed under the terms and conditions of the Creative Commons Attribution (CC BY) license (https:// creativecommons.org/licenses/by/ 4.0/).

The sCO<sup>2</sup> cycle is believed to be applied for fossil combustion power [7,8], heat recovery [9,10], solar thermal power [11,12], and generation IV nuclear reactors [13,14], and can even be combined with other cycles [15]. Among these heat sources, the newgeneration nuclear reactor is regarded as a major source of sustainable energy, with a tremendous capacity, near-zero emissions, and multipurpose products [16]. Previous studies [17] revealed that the sCO<sup>2</sup> Brayton cycle can be combined with the helium-cooled fast reactor [18,19], the sodium-cooled fast reactor (SFR) [20], the lead–bismuth fast reactor, and the high-temperature gas reactor. The SFR, which is the fastest-growing reactor type, has several demonstration reactors in different countries. Therefore, it is regarded as the quickest route to applying the sCO2. As a heat source, the SFR has a limited range at moderate temperatures. The sCO<sup>2</sup> Brayton cycle has been demonstrated to be well-suited to a combination with the SFR in previous studies [21]. The specifications considering the temperature of the secondary sodium loop are as follows: 550 ◦C/395 ◦C with the Advanced Fast Reactor (AFR) [22], 520 ◦C/335 ◦C with the Japan Atomic Energy Agency Sodium Fast Reactor (JSFR) [23], and 520 ◦C/350 ◦C with the China Experimental Fast Reactor (CEFR). Considering power class, CEFR-1200 has four cycles with 300 MW per cycle, AFR-100 can output 100 MWe, and the electricity output of JSFR is 1500 MWe with two loops. A certain number of kWe/Mwe-class space reactors are also currently being developed. The sCO<sup>2</sup> Brayton cycle fits the temperature gap of the secondary sodium inlet and outlet at 155–185 ◦C. Moreover, sCO<sup>2</sup> could avoid sodium–water interactions considering the safety aspect and operational advantages. Thus, replacing the steam Rankine cycle with the sCO<sup>2</sup> Brayton cycle with high conventional loop pressure could increase the safety of the system. In general, combined with the SFR, the sCO<sup>2</sup> Brayton cycle is used as a conventional loop, which is well-adapted to the reactor [21] regarding the temperature gaps and ranges of heat exchange processes [17]. The AFR–100 can reach a higher efficiency of 42.3% and 104.9 MW net power with the sCO<sup>2</sup> Brayton cycle [21].

The recuperation cycle is the preliminary layout of the sCO<sup>2</sup> Brayton cycle, as shown in Figure 1. The conventional loop includes the Na-sCO<sup>2</sup> heat exchanger as the heat source, turbine, recuperator, cooler, and compressor. Unlike the steam Rankine cycle, the sCO<sup>2</sup> Brayton cycle must have a recuperation process to avoid heat waste of the hightemperature working fluid from the turbine outlet. The system performance in terms of the cycle efficiencies of the recuperation cycle remains unsatisfactory. A recuperation cycle with a concise structure was adopted as a reference for the system design and performance analysis. The recompression cycle, the partial-cooling cycle, and even substantially complex structures were considered to realize an improved system performance [24–26]. Aside from layouts, operation parameters, such as working fluid pressures, temperatures, and recuperated points, affect the system efficiency remarkably [27].

**Figure 1.** Layouts of the SFR-sCO<sup>2</sup> recuperation cycle. a–h represent state points of working fluid in the cycle.

Moreover, applying the sCO<sup>2</sup> Brayton cycle is expected to reduce the capital cost per unit output electrical power of the nuclear power plant or the levelized cost of electricity [17]. Exergy analysis shows that the highest exergy loss takes place in the heliostat field, at nearly 42.5% of incident solar exergy, with a recompression Brayton cycle with partial-cooling and an improved heat recovery (RBC-PC-IHR) configuration [28]. Exergoeconomic analysis was applied to sCO<sup>2</sup> power systems with several configurations of the turbine inlet temperature and cooling system. The recompression concept and the novel cycle showed the best performance [29]. With the recompression cycle, the maximum exergy efficiency reached about 55% in previous reports, and that using the CO2-C7H<sup>8</sup> binary mixture was nearly 60% [5]. Previous research has already performed exergoeconomic investigation of the sCO2-SFR with the recompression cycle [30]. However, the exergoeconomics of the partialcooling cycle of the SFR has not been presented.

The system performance and economic analyses of the sCO<sup>2</sup> Brayton cycle, particularly for the SFR with the partial-cooling layout, are discussed in the current research. The energetic, exergetic, and exergoeconomic analyses are presented, and the optimized results are compared with the recompression cycle. The sensitivity analyses mainly focus on the effect of the pressure and temperature ranges.

### **2. Analysis Methods**

### *2.1. Energetic Analysis*

The sCO<sup>2</sup> power cycle includes heat exchangers, turbomachinery, pipes, and valves. The balance equation of heat exchangers is as follows:

$$
\dot{Q}\_{HX} = \dot{m}\_{\text{hot}} \Delta h\_{\text{hot}} = \dot{m}\_{\text{cold}} \Delta h\_{\text{cold}} \tag{1}
$$

The balance equation of turbomachinery is as follows:

$$
\dot{\mathcal{W}} = \dot{m}\_{\text{CO}\_2} \Delta h \tag{2}
$$

The thermal efficiency of the cycle is as follows:

$$
\eta\_{\text{cyc}} = \frac{\dot{W}\_{\text{net}}}{\dot{Q}\_{InCycle}} \tag{3}
$$

where *QInCycle* represents the heat transferred to the sCO<sup>2</sup> via the Na-sCO<sup>2</sup> heat exchanger, and . *Wnet* is the net power outputted from the cycle. The pressure loss of pipes and valves is not considered.

### *2.2. Exergetic Analysis*

.

The exergetic analysis elucidates the route and the amount of the exergy lost with the same simulation results [4]. The exergy of the working fluid stream can be expressed as follows:

$$e\_{\rm sCO\_2} = h - h\_a - T\_a(s - s\_a) \tag{4}$$

The exergy rate of the working fluid stream can be expressed as follows:

$$
\dot{E}\_{\text{sCO}\_2} = \dot{m}\_{\text{sCO}\_2} e\_{\text{sCO}\_2} \tag{5}
$$

The exergy loss for heat exchangers can be calculated by the following:

$$
\dot{E}\_{\rm loss} = \Delta \dot{E}\_{\rm hot} - \Delta \dot{E}\_{\rm cold} = \left(\dot{E}\_{\rm hot,in} - \dot{E}\_{\rm hot,out}\right) - \left(\dot{E}\_{\rm cold,out} - \dot{E}\_{\rm cold,in}\right) \tag{6}
$$

For the turbine, the exergy loss can be calculated as follows:

$$
\dot{E}\_{\text{loss,turbine}} = \Delta \dot{E}\_{\text{turbine}} - \dot{\mathcal{W}}\_{\text{turbine}} = \dot{E}\_{\text{turbine},\text{in}} - \dot{E}\_{\text{turbine},\text{out}} - \dot{\mathcal{W}}\_{\text{turbine}} \tag{7}
$$

The exergy loss for compressors can be calculated as follows:

$$
\dot{E}\_{\text{loss,comp}} = \dot{\mathcal{W}}\_{\text{comp}} - \Delta \dot{E}\_{\text{comp}} = \dot{\mathcal{W}}\_{\text{comp}} - \left(\dot{E}\_{\text{comp},out} - \dot{E}\_{\text{comp},in}\right) \tag{8}
$$

The exergy efficiency of the cycle is computed as follows:

$$
\eta\_{exe,cyc} = \frac{\dot{W}\_{net}}{\dot{E}\_{InCycle}} \tag{9}
$$

where . *EInCycle* represents the exergy transferred to the sCO<sup>2</sup> via the Na-sCO<sup>2</sup> heat exchanger.

### *2.3. Exergoeconomic Analysis*

Economic analysis is an essential aspect of evaluating technical applications. Exergoeconomic analysis is used for the establishment of a guideline of the cost per exergy unit. Specifically, the exergy costing method, which is simple and direct, is widely used in the field of exergoeconomic analysis [31–33]. The exergy costing method was selected for this study, and the results were analyzed in combination with energetic and exergetic calculations.

The cost balance equation for the *k*th component in a power conversion system is as follows [30]:

$$\sum \left( c\_{\text{out}} \dot{E}\_{\text{out}} \right)\_k + c\_{W,k} \dot{W}\_k = \sum \left( c\_{\text{in}} \dot{E}\_{\text{in}} \right)\_k + c\_{q,k} \dot{E}\_k + \dot{Z}\_k \tag{10}$$

The cost rate of the overall system ( *Ctotal*) is the sum of capital investment, operation and maintenance costs ( . *Z*, in Table 1), and the cost derived from exergy loss and destruction ( . *CL*+*D*), as follows: . . .

$$\mathbb{C}\_{total} = Z + \mathbb{C}\_{L+D} \tag{11}$$

**Table 1.** Cited data for cost of components.


The definitions of "fuel" and "product" considering the partial-cooling cycle are summarized in Table 2. In addition, the solution for a set of equations is provided in Table 3.


**Table 2.** Fuel–product definition of the partial-cooling cycle.

**Table 3.** Exergetic cost rate balance and auxiliary equations for the partial-cooling cycle.


Following the previous research [30], the primary circuit, the second loop, and the Na-sCO<sup>2</sup> heat exchanger were categorized as the "Reactor core". . *Cf uel* represents the fuel cost rate of the entire part and can be calculated as follows:

$$
\dot{\mathbf{C}}\_{fuel} = \mathbf{c}\_{fuel} \dot{\mathbf{Q}}\_{core} \tag{12}
$$

where *c f uel* is the fuel cost (USD/(MW·h)). *c f uel* was set as 7.4 USD/(MW·h) based on the mean value comparison of the constant dollar unit costs between the fast reactors and the gas-cooled reactor [33,37–39].

### *2.4. Solution Procedures*

A system simulation program (The original program was developed by Harbin Electric Company Limited, and the Software Copyright Registration Number is 2018SR349409) was developed with the functions energy and exergy balance calculations, parameter sensitivity analyses, and system performance optimizations. Multiobjective optimization was performed using a genetic algorithm developed in Python 3 (Figure 2), which was crosschecked with an enumeration algorithm. A genetic algorithm begins with randomly selected values of parameters (as the initial population). Then, each parameter is evaluated via fitness calculation to test its ability to solve a problem. The selection operation selects some of the parameters for reproduction. The biological crossing over and recombination of parameters are conducted in coupling and mutation operation. Then, a new population is used in a new calculation until the operation objectives are attained. Table 4 shows the manipulated parameters in the optimization. The optimization aims to obtain the

maximum value of *ηexe*,*cyc* or the minimum value of *Ctotal*. The split ratios in the cycle are adjusted based on the optimization process in the range of 0.1–0.9 to obtain the best result. It is one of the optimization parameters, and it is manipulated as other parameters in the genetic algorithm and the enumeration algorithm.

**Figure 2.** Flow diagram of genetic algorithm method.

**Table 4.** Manipulated parameters in the optimization.


### **3. Results and Discussions**

### *3.1. Energy and Exergy Analyses with Different Layouts*

The heat and work distribution of the recuperation cycle based on the energy and exergy analyses in previous studies is shown in Figure 3a. The heat flow map indicates that the heat flow rate into the cycle ( . *Qin*) was set as the reference quantity of energy. The power input was 0.137 . *Qin* when 1 . *Qin* energy came into the cycle to support the sCO<sup>2</sup> compression. As the output energy, the turbine output 0.473 . *Qin* as power, while the energy released 0.664 . *Qin* from the cooler. The heat flow rate of the recuperator in the recuperation process, which is an enormous heat exchange process, was 1.497 . *Qin*. The cooler wasted a considerable amount of energy according to the heat flow map. However, the discharging energy from the cooler could not be reused due to the low pressure and temperature.

**Figure 3.** Energy and exergy distributions of the recuperation cycle [25]. (**a**) Heat and power, (**b**) Exergy and exergy loss. A–h represent state points of working fluid in the cycle.

The exergy flow map and the exergy losses of the process to improve the cycle structure are illustrated and shown in Figure 3b. The exergy flow rate into the cycle ( . *Ein*) was set as the reference quantity of exergy in the exergy flow map. The input exergies were 1 . *Ein* and 0.23 . *Ein* from the heat source and the compression process, respectively. The main output exergy was 0.81 . *Ein* via the turbine. Exergy losses mainly occurred in the recuperation, cooling, and heat exchange in the heat source processes as 0.17 . *Ein*, 0.10 . *Ein*, and 0.06 . *Ein*, respectively. Most exergy losses occurred in the heat exchange processes; thus, many types of cascade cycles could be adopted to reduce the exergy losses. Among these cycles, the recompression cycle, which is known as the Feher cycle, had good performance application in the sCO<sup>2</sup> Brayton cycle with the SFR, as shown in Figure 4a. Moreover, the partial cooling in Figure 4b had a relatively simple structure and good performance compared to the compression cycle. The energy and exergy performance of the compression cycle were analyzed in the previous research. The current research focuses on the study of the partial-cooling cycle and completes its comparison with the compression cycle.

**Figure 4.** Advanced cycle layouts of sCO<sup>2</sup> -SFR. (**a**) Recompression cycle, (**b**) partial cooling cycle. a–n represent state points of working fluid in the cycle.

### *3.2. System Performance of the Partial-Cooling Cycle*

The optimization of the sCO2-SFR with the partial-cooling layout at the highest exergy efficiency reaching 63.65% with a net power output of 34.39 MW is shown in Figure 5. A series of parameter limitations was set during the optimization based on the engineering practice, as listed in Table 4.

**Figure 5.** Optimal simulation results of the partial-cooling cycle with sCO<sup>2</sup> -SFR. a–n represent state points of working fluid in the cycle.

Figure 6 shows the *T*-*s* diagram of the recompression [30] and partial-cooling cycle with optimization results. Compared with the recompression cycle, the compression processes are more complex, including three parts. In the partial-cooling cycle, the pressure of the working fluid was raised in the main compressor (a–b). A part of sCO<sup>2</sup> was cooled in the subcooler (k–l), and the recompressor LT further raised the working fluid pressure (l–m),

and then the temperature of sCO<sup>2</sup> was increased in the recuperator LT (m–n). The other part of sCO<sup>2</sup> from the main compressor went into the recompressor HT (g–h) without the cooling process. Both sCO<sup>2</sup> streams entered the mixer with roughly comparable temperatures. sCO<sup>2</sup> went into the recuperator HT to recycle the heat (i–c) after the mixing, and then the working fluid absorbed heat from the heat source of the conventional loop (c–d). Afterward, the working fluid stream with a high temperature and pressure expanded in the turbine (d–e) outputting power. Processes e–j, j–f, and f–a are the heat discharges in the recuperator HT, the recuperator LT, and the main cooler, respectively.

**Figure 6.** *T*-*s* diagram at the optimum point with the advanced cycles. (**a**) Recompression cycle, (**b**) partial cooling cycle. a–n represent state points of working fluid in the cycle.

The following observations are presented in Table 5: a 3.57 MW exergy loss from the heat source of the conventional loop (6.61%∆ . *Ein*), a 5.82 MW exergy loss from the recuperators (10.77%∆ . *Ein*), a 4.38 MW exergy loss from the coolers (8.10%∆ . *Ein*), a 3.60 MW exergy loss from the turbine (6.67%∆ . *Ein*), and a 2.27 MW exergy loss from the compressors (4.21%∆ . *Ein*). Table 5 also reveals that the exergy losses from the Na-sCO<sup>2</sup> heat exchanger were greater in the partial-cooling cycle than in the recompression cycle due to the wide temperature gap between the two sides of the exchanger. Moreover, additional exergy loss was observed from these coolers due to the subcooler application in the partialcooling cycle.


**Table 5.** Comparisons of exergy losses between the partial-cooling and recompression cycles.

### *3.3. Effects of Operation Parameters on Cycle Efficiencies*

The cycle efficiencies are discussed on the basis of sensitivity analysis results. The sensitivity of efficiencies to the main system parameters, including the pressure ratio (*β* = *pH*/*pL*), the inlet temperature of the main compressor (*Tmin*), and the inlet temperature of the turbine (*Tmax*), was analyzed.

3.3.1. Pressure Ratio

*β* was set in the range of [2.00, 3.50] with the *pcomp*,*in* = 8.00 MPa, *Tmin* = 35.00 ◦C, *<sup>T</sup>max* = 480.00 ◦C, and . *mCO*<sup>2</sup> = 350.00 kg/s. Theoretically, the maximum *β* could be reached at a high *pH*. However, realizing a high *p<sup>H</sup>* is difficult under the current situation of compressor technology. Therefore, only the calculation with the *β* range in [2.00, 3.50] is shown in this section.

The cycle efficiencies (*ηcyc* and *ηexe*,*cyc*) of the partial-cooling cycle were generally lower than those of the recompression cycle, as shown in Figure 7, but the gap was narrowed with the increase in *β.* The effect tendencies of *β* on *ηcyc* and *ηexe*,*cyc* were based on the partial-cooling cycle rise with the increase in *β* from 32.51% to 36.53% and from 54.90% to 63.65%, respectively. If the value of *β* can be raised, then superior system efficiencies could be reached. Unlike the partial-cooling cycle, the maximum value of *ηcyc* at *β* = 2.75 was 37.96%, and that of *ηexe*,*cyc* at *β* = 3.00 was 64.84% as observed in the specified *β* range in the recompression cycle. Therefore, a high *β* would not elicit a superior system performance in the recompression cycle case.

**Figure 7.** Effects of *β* on *ηcyc* and *ηexe*,*cyc* with the partial-cooling cycle compared with the recompression cycle.

### 3.3.2. Inlet Temperature of the Main Compressor

*Tmin* cannot be less than 32.00 ◦C (close to the critical point) because only the supercritical Brayton cycle was considered in this study. The range of *Tmin* was decided to fall within [32.00, 36.00] ◦C with *β* = 2.75, *pcomp*,*in* = 8.00 MPa, *Tmax* = 480.00 ◦C, and . *mCO*<sup>2</sup> = 428.57 kg/s. Figure 8 shows that the cycle efficiencies of the partial-cooling cycle were better stabilized under *Tmin* than the recompression cycle. *ηcyc* increased initially and decreased from 35.94% to 36.06% (maximum value, at *Tmin* = 35.00 ◦C), then to 35.37% under the partial-cooling cycle. Similarly, *ηexe*,*cyc* initially rose from 61.68% to 62.31% (maximum value, at *Tmin* = 35.00 ◦C) and then dropped to 61.70%. As discussed in Section 3.3.1, the decreasing *Tmin* not only reduced the outlet temperature of the compressor, leading to high efficiencies, but also enhanced the heat loss from the subcooler, resulting in energy and exergy losses of steam due to the application of the subcooler. Optimized *Tmin*, which could maximize the efficiencies, was elicited by the aforementioned influences.

**Figure 8.** Effects of *Tmin* on *ηcyc* and *ηexe*,*cyc* with the partial-cooling cycle compared with the recompression cycle.

### 3.3.3. Inlet Temperature of Turbine

Figure 9 shows that the range of *Tmax* was decided to fall within [430.00, 480.00] ◦C with *<sup>β</sup>* = 3.5, *<sup>p</sup>comp*,*in* = 8.00 MPa, *<sup>T</sup>min* = 35.00 ◦C, and . *mCO*<sup>2</sup> = 350.00 kg/s. *ηcyc* and *ηexe*,*cyc* linearly increased with *Tmax* regardless of the partial-cooling or the recompression cycle. *ηcyc* increased by 2.79% from 33.74% to 36.53% under the partial-cooling cycle, whereas *ηexe*,*cyc* dramatically rose by 5.19% from 58.46% to 63.65%. These variations indicate that *Tmax* is essential to obtain high *ηcyc* and *ηexe*,*cyc*. The highest *Tmax* reached in the current research was 480 ◦C due to the temperature limit of the SFR core (the outlet temperature of the core is close to 550 ◦C).

**Figure 9.** Effects of *Tmax* on *ηcyc* and *ηexe*,*cyc* with the partial-cooling cycle compared with the recompression cycle.

The partial-cooling cycle showed a good system performance with the optimization results and the sensitivity analysis. The exergoeconomic of the two layouts will be analyzed in the next section for further comparison.

### *3.4. Exergoeconomic Discussion*

The effects of system parameters on exergoeconomic are initially analyzed in this section. The exergoeconomic optimized results of the partial-cooling cycle are then summarized and compared with the recompression cycle.

### 3.4.1. Pressure Ratio

Pressure ratio (*β*) is a major factor causing cost variation. A large *β* results in a high outlet pressure of the compressor with the same inlet pressure. Thus, a high outlet pressure would provide additional power support to the compressor. Moreover, the cost of the compressor and the turbine increased in accordance with the equations in Table 1. Figure 10 shows that *β* was within the range [2.00, 3.50] with *pcomp*,*in* = 8.00 MPa, *<sup>T</sup>min* = 35.00 ◦C, *<sup>T</sup>max* = 480.00 ◦C, and . *mCO*<sup>2</sup> = 428.57 kg/s. . *Ctotal* dropped 261.19 USD/h from 2491.55 USD/h to 2230.36 USD/h with the partial-cooling cycle. Meanwhile, both efficiencies continuously increased.

**Figure 10.** Effects of β on . *Ctotal* with the partial-cooling cycle compared with the recompression cycle.

. *Ctotal* comprises capital investment, operation, and maintenance costs ( . *Z*), and the cost from exergy loss and destruction ( . *CL*+*D*). The effect of *β* on . *CL*+*<sup>D</sup>* is generally larger than that on . *Z*, and the variation in . *CL*+*<sup>D</sup>* with *β* introduces changes in . *Ctotal*. Considering . *Z*, the increase in *β* indicates that the maximum cycle pressure would be high, further causing additional . *Z* of compressors and turbines. Therefore, . *Z* slightly increased with the rise in *β*, as shown in Figure 11. Unlike . *Z*, the variation in . *CL*+*<sup>D</sup>* is complicated due to exergy loss and destruction in the partial-cooling cycle, and . *CL*+*<sup>D</sup>* significantly dropped initially and then declined from 984.35 USD/h to 660.20 USD/h.

**Figure 11.** Effects of *β* on . *Z* and . *CL*+*<sup>D</sup>* with the partial-cooling cycle. **Figure 11.** Effects of *β* on ሶ and ሶ ା with the partial-cooling cycle.

. *Ccomponent* is the total cost of each component, such as the compressor, the cooler, the turbine, the recuperator, and the Na-sCO<sup>2</sup> heat exchanger. As seen in Figure 12, the total cost of the Na-sCO<sup>2</sup> heat exchanger barely changed with *β* maintaining a value of around 1570–1580 USD/h. The total costs of other components are shown in Figure 12. Turbines and compressors had a lower cost at lower *β*. By contrast, the total cost of recuperators decreased with increasing *β*. With higher *β*, the exergy of the working fluid at the outlet of turbine decreased, as did the energy needed for recuperation. Therefore, the total cost of recuperator was reduced. ሶ ௧ is the total cost of each component, such as the compressor, the cooler, the turbine, the recuperator, and the Na-sCO2 heat exchanger. As seen in Figure 12, the total cost of the Na-sCO2 heat exchanger barely changed with *β* maintaining a value of around 1570–1580 USD/h. The total costs of other components are shown in Figure 12. Turbines and compressors had a lower cost at lower *β*. By contrast, the total cost of recuperators decreased with increasing *β*. With higher *β*, the exergy of the working fluid at the outlet of turbine decreased, as did the energy needed for recuperation. Therefore, the total cost of recuperator was reduced.

**Figure 12.** Effects of β on ሶ ௧ with the partial-cooling cycle. **Figure 12.** Effects of β on . *Ccomponent* with the partial-cooling cycle.

### 3.4.2. Inlet Temperature of the Main Compressor 3.4.2. Inlet Temperature of the Main Compressor

Considering the effect of , the range of was decided to fall within [32.00, 38.00] °C when *β* = 3.00, , = 8.00 MPa, ௫ = 480.00 °C, and ሶ ைమ = 350.00 kg/s. The ሶ ௧௧ of the partial-cooling cycle was significantly higher than that of the recompression cooling cycle. This value decreased from 2308.44 USD/h to 2249.50 USD/h when increased from 32.00 °C to 36.00 °C, and then remained around 2250 USD/h with the increase in , as shown in Figure 13. Considering the effect of *Tmin*, the range of *Tmin* was decided to fall within [32.00, 38.00] ◦C when *<sup>β</sup>* = 3.00, *<sup>p</sup>comp*,*in* = 8.00 MPa, *<sup>T</sup>max* = 480.00 ◦C, and . *mCO*<sup>2</sup> = 350.00 kg/s. The . *Ctotal* of the partial-cooling cycle was significantly higher than that of the recompression cooling cycle. This value decreased from 2308.44 USD/h to 2249.50 USD/h when *Tmin* increased from 32.00 ◦C to 36.00 ◦C, and then remained around 2250 USD/h with the increase in *Tmin*, as shown in Figure 13.

**Figure 13.** Effects of *Tmin* on . *Ctotal* with the partial-cooling cycle compared with the recompression cycle.

Figure 14 shows that the variation in . *Ctotal* was caused by the change in . *CL*+*D*, and . *Z* barely changed with *Tmin*. As the inlet of the compressor, *Tmin* increased the outlet temperature of the compressor with the same pressure ratio in the range of [32.00, 38.00] ◦C in the partial-cooling cycle. However, temperatures were not the major influencing factors on . *Z* according to the equations in Table 1. By contrast, *Tmin* can affect the variations in exergy loss and destruction in the entire system. . *CL*+*<sup>D</sup>* decreased by 60.55 USD/h from 759.31 USD/h to 698.76 USD/h when *Tmin* varied from 32.00 ◦C to 36.00 ◦C, and then remained at approximately 700 USD/h. . *CL*+*<sup>D</sup>* continued to decrease with the increase in *Tmin* when *Tmin* was less than 35.00 ◦C.

**Figure 14.** Effects of *Tmin* on . *Z* and . *CL*+*<sup>D</sup>* with the partial-cooling cycle.

Figure 15 shows the variation in component total cost with *Tmin*. *Tmin* hardly affected the total cost of turbines and compressors. The total cost of the Na-sCO<sup>2</sup> heat exchanger barely changed with *β* maintained around 1564–1584 USD/h. The total cost of the recuperator continued to decrease with the increase in *Tmin*. During the compression process, a higher outlet temperature of the compressor could be obtained with higher *Tmin*. The former narrowed the temperature gap of the recuperators. Therefore, the heat exchange capacity and the cost of recuperators were reduced.

**Figure 15.** Effects of on ሶ ௧ with the partial-cooling cycle. **Figure 15.** Effects of *Tmin* on . *Ccomponent* with the partial-cooling cycle.

### 3.4.3. Inlet Temperature of Turbine

3.4.3. Inlet Temperature of Turbine Figure 16 shows that the range of ௫ was decided to fall within [430.00, 480.00] °C when *<sup>β</sup>* = 3.50, , = 8.00 MPa, = 35.00 °C, and ሶ ைమ = 350.00 kg/s. The ሶ variation lines linearly declined with the increase in ௫, from 2251.67 USD/h to 2088.88 USD/h (for the recompression cycle) [30] and from 2392.85 USD/h to 2230.36 USD/h (for the partial-cooling cycle). Increasing ௫ was one of the most effective approaches to reducing the total cost considering system efficiencies. However, the heat source temperature for SFR limited the ௫ of the sCO2 cycle. High ௫ could be reached in the fu-Figure 16 shows that the range of *Tmax* was decided to fall within [430.00, 480.00] ◦C when *<sup>β</sup>* = 3.50, *<sup>p</sup>comp*,*in* = 8.00 MPa, *<sup>T</sup>min* = 35.00 ◦C, and . *mCO*<sup>2</sup> = 350.00 kg/s. The . *Ctotal* variation lines linearly declined with the increase in *Tmax*, from 2251.67 USD/h to 2088.88 USD/h (for the recompression cycle) [30] and from 2392.85 USD/h to 2230.36 USD/h (for the partial-cooling cycle). Increasing *Tmax* was one of the most effective approaches to reducing the total cost considering system efficiencies. However, the heat source temperature for SFR limited the *Tmax* of the sCO<sup>2</sup> cycle. High *Tmax* could be reached in the future with the optimization of the SFR core design and the performance enhancements of the Na-sCO<sup>2</sup> heat exchanger.

௧௧

430 440 450 460 470 480 0.25 1800 *Ctotal,recomp* **Figure 16.** Effects of *Tmax* on *ηcyc*, *ηexe*,*cyc*, and . *Ctotal* with the partial-cooling cycle compared with the recompression cycle.

*Ctotal*(\$/h)

.

barely changed with ௫.

Inlet Temperature of Turbine (°C)

Similar to the effect of *β* and , Figure 17 shows that ሶ

**Figure 16.** Effects of ௫ on ௬ , ௫,௬ , and ሶ ௧௧ with the partial-cooling cycle compared with the recompression cycle. Similar to the effect of *β* and *Tmin*, Figure 17 shows that *Z* barely changed with *Tmax*. . *CL*+*<sup>D</sup>* dropped because the increase in *Tmax* reduced the exergy loss and the destruction of the cycle from 823.42 USD/h to 660.20 USD/h for the partial-cooling cycle.

of the cycle from 823.42 USD/h to 660.20 USD/h for the partial-cooling cycle.

ା dropped because the increase in ௫ reduced the exergy loss and the destruction

ሶ

**Figure 17.** Effects of *Tmax* on . *Z* and . *CL*+*<sup>D</sup>* with the partial-cooling cycle.

Figure 18 shows the variation in component total costs with *Tmax*. *Tmax* barely affected the total cost of turbines and compressors. The total cost of the compressor, cooler, turbine, and recuperator barely changed with *Tmax*. However, the total cost of the Na-sCO<sup>2</sup> heat exchanger was significantly affected by *Tmax*. The total cost of the recuperator decreased by increasing *Tmax*; the former dropped about 155.36 USD/h when *Tmax* changed from 430 ◦C to 480 ◦C.

**Figure 18.** Effects of *Tmax* on *Ccomponent* with the partial-cooling cycle. (**a**) Multiple components, (**b**) Na-sCO<sup>2</sup> heat exchanger.

The comparison among *β*, *Tmin*, and *Tmax* revealed that the change in . *CL*+*<sup>D</sup>* with *β* was substantially larger than that with *Tmax* or *Tmin*. Thus, manipulating *β* is important to guarantee the good economy of the system. Moreover, the sum of capital investment, operation, and maintenance costs ( . *Z*) accounted for large proportions of the total cost rate, which was almost double that of . *CL*+*<sup>D</sup>* in each condition.

### *3.5. Comparison Summary of the Two Layouts*

.

The partial-cooling cycle showed good system performance with high efficiency and net power via the optimization process based on the operation conditions of the SFR in this study.

Compared with the recompression cycle, the exergy losses from the Na-sCO<sup>2</sup> heat exchanger were greater in the partial-cooling cycle due to the wide temperature gap between the two sides of the exchanger. Moreover, the coolers demonstrated additional exergy losses due to the subcooler application in the partial-cooling cycle.

Furthermore, the recompression cycle could slightly improve the exergoeconomic performance compared to the partial-cooling cycle. The minimum . *Ctotal* of 2230.36 USD/h with *ηexe*,*cyc* = 63.65% could be obtained for the partial-cooling cycle, where *β* = 3.50, *Tmin* = 35.00 ◦C, and *Tmax* = 480.00 ◦C. Similarly, the minimum . *Ctotal* reached 2088.88 USD/h with *ηexe*,*cyc* = 64.72% at *β* = 2.75 for the recompression cycle [30]. Meanwhile, the partialcooling cycle showed good potential for reducing the total cost by increasing the pressure ratio with the development of sCO<sup>2</sup> technology.

### **4. Conclusions**

The current research investigated the system performance and carried out economic analysis of the sCO<sup>2</sup> Brayton cycle for the SFR with a partial-cooling layout. The exergy efficiency of the partial-cooling cycle reached 63.65% with a net power output of 34.39 MW after optimization, and the minimum . *<sup>C</sup>total* was 2230.36 USD/h. Similarly, the minimum . *Ctotal* reached 2088.88 USD/h with *ηexe*,*cyc* = 64.72% at *β* = 2.75 for the recompression cycle. Compared with the recompression cycle, the exergy losses from the Na-sCO<sup>2</sup> heat exchanger were greater in the partial-cooling cycle due to the wide temperature gap between its two sides. Moreover, the coolers had additional exergy losses due to the subcooler application in the partial-cooling cycle.

The cost derived from exergy loss and destruction in the selected ranges of parameters were significantly affected by the pressure ratio and the inlet temperatures of the main compressor and the turbine. The change in cost from exergy loss and destruction with the pressure ratio was substantially greater than that from the inlet temperature of the turbine or the inlet temperature of the main compressor. The total cost of recuperators decreased with the increase in *β*, *Tmin*. In addition, the total cost of the recuperator could be reduced by increasing *Tmax*. Therefore, manipulating *β* is important to guarantee the good economy of the system. Moreover, the capital investment and operation and maintenance costs normally accounted for large proportions of the total cost rate, which was almost double the cost from exergy loss and destruction in each condition. The partial-cooling cycle obtained the minimum total cost rate when the pressure ratio was equal to 3.50. The inlet temperatures of the main compressor and the turbine were 35 ◦C and 480 ◦C, respectively.

**Author Contributions:** Writing—original draft preparation and investigation, M.X.; investigation and resource, J.C.; supervision, X.R.; writing—review and editing, S.W.; Visualization, P.C.; project administration, C.Z. All authors have read and agreed to the published version of the manuscript.

**Funding:** This research was funded by the National Key Research and Development Program of China grant number 2020YFF0218100 and Natural Science Foundation of Heilongjiang Province of China grant number YQ2020E032. And the APC was funded by the National Key Research and Development Program of China grant number 2020YFF0218100.

**Institutional Review Board Statement:** Not applicable.

**Informed Consent Statement:** Not applicable.

**Data Availability Statement:** Not applicable.

**Acknowledgments:** We thank Zhongyuan Ma of the Nuclear Power Division, Harbin Electric Company Limited, for his assistance with the Sodium Fast Reactor System.

**Conflicts of Interest:** The authors declare no conflict of interest.

### **Nomenclature**

### **Symbols**


### **References**

