On-Board Liquid Hydrogen Cold Energy Utilization System for a Heavy-Duty Fuel Cell Hybrid Truck

In this paper, a kind of on-board liquid hydrogen (LH2) cold energy utilization system for a heavy-duty fuel cell hybrid truck is proposed. Through this system, the cold energy of LH2 is used for cooling the inlet air of a compressor and the coolant of the accessories cooling system, sequentially, to reduce the parasitic power, including the air compressor, water pump, and radiator fan power. To estimate the cold energy utilization ratio and parasitic power saving capabilities of this system, a model based on AMESim software was established and simulated under different ambient temperatures and fuel cell stack loads. The simulation results show that cold energy utilization ratio can keep at a high level except under extremely low ambient temperature and light load. Compared to the original LH2 system without cold energy utilization, the total parasitic power consumption can be saved by up to 15% (namely 1.8 kW).


Introduction
With the development of the fuel cell electric vehicle (FCEV), there has been an increasing demand for a hydrogen source with high energy density. The common hydrogen sources of on-board hydrogen storage and supply systems are high-pressure hydrogen (35 MPa and 70 MPa), low-temperature liquid hydrogen (LH 2 ), and metal hydride [1,2]. Among them, the first two methods are more commonly used. Furthermore, the density of liquid hydrogen (10 bar, 31 K, 50 kg/m 3 ) is about 2.2 times higher than that of 35 MPa high-pressure gas hydrogen (23 kg/m 3 ) at room temperature, and 1.35 times that of 70 MPa gas hydrogen (37 kg/m 3 ) at room temperature [3]. As for the liquid hydrogen tank, its weight density is at least 9 wt%, while these examples of 35 MPa and 70 MPa hydrogen storage solutions are just 2.5 wt% and 4.5 wt%, respectively. In addition, the storage and transportation costs of liquid hydrogen are also much lower than compressed hydrogen [4]. Therefore, liquid hydrogen is widely considered a competitive hydrogen source, especially for heavy-duty, long-distance vehicles. However, the liquefaction process consumes a large amount of energy, which is the main drawback of LH 2 . The actual specific energy consumption of liquefaction is typically about 12-15 kWh per kg LH 2 [5,6], and that of an advanced process could reach about 5-6 kWh per kg LH 2 [7,8]. In order to increase the overall efficiency of LH 2 , it is important to recover part of the liquefaction energy.
As for the cold energy utilization, there has been some research in the field of liquid natural gas (LNG), which has been widely used in energy storage and is similar to LH 2 in its physical properties. LNG cold energy is mainly utilized for air separation, desalination processes, cryogenic carbon dioxide capture, and power generation [9]. More specifically, there are several power generation cycles, including the gas turbine cycle, organic Rankine cycle, Brayton cycle, and combined cycle [10]. Liu et al. proposed an innovative combined cooling, heating, and power system (CCHP) based on the SOFC/GT/CO 2 cycle and the organic Rankine cycle with LNG cold energy utilization to achieve cascade energy utilization and carbon dioxide capture. The results illustrated that the comprehensive energy utilization, the net power generation, and the overall exergy efficiencies of the system could reach about 79.48%, 79.81%, and 62.29%, respectively [11]. However, these systems are mainly designed for large regasification terminals, and the applications are not consistent with the requirements of vehicles.
Due to the lack of large application, little research have focused on the cold energy utilization of LH 2 . Trevisani et al. proposed and compared gas turbine and magnetohydrodynamics based energy recovery systems that produce electric energy [12]. Zhang et al. established a novel Brayton cycle with the integration of LH 2 cryogenic exergy utilization, which can reach high energy and exergy efficiency (73% and 45%, respectively) [13]. However, these systems need gas turbines and additional working fluids, which make them difficult to realize for their on-board application. Few researchers have been able to draw on any systematic research into on-board liquid hydrogen cold energy utilization systems adapted vehicles using LH 2 as fuel.
In this paper, a kind of on-board liquid hydrogen cold energy utilization system is proposed. Considering the cooling demand of fuel cell vehicles and the restriction of space and engineering feasibility, the cold energy of LH 2 in the evaporation process is directly used for cooling the inlet air of compressor and the coolant of the accessories cooling system through a vaporizer to reduce the parasitic power, including the air compressor, water pump, and radiator fan power. Then, the cold energy utilization ratio and parasitic power saving capabilities under different ambient temperatures and fuel cell stack loads are compared and analyzed.

Configuration Design
In our previous studies [4], a kind of LH 2 system, named as the original LH 2 system, is proposed and produced; moreover, it has been applied in heavy-duty fuel cell hybrid trucks. The scheme and equipment of original LH 2 systems are respectively shown in Figures 1 and 2. As for this system, the vaporizer consists of two parts, namely the heat exchanger 1 (HEX-1) and heat exchanger 2 (HEX-2). LH 2 firstly passes through HEX-1 and be heated directly by the ambient air to reach from about −40 • C to 20 • C. Then, H 2 passes through HEX-2 and be further heated by the coolant in the accessories cooling system. HEX-2 is necessary for the system because H 2 from the outlet of HEX-1 cannot maintain a proper temperature due to the great change of ambient temperature in different seasons. The accessories cooling system takes away the heat of the DC/DC and compressed air, and releases it to low temperature H 2 and the environment. According to a previous joint test of this system and the fuel cell system, the liquid hydrogen system had the ability to keep the pressure relatively stable at different working conditions and could meet the gas supply requirements of the fuel cell stack [4]. However, unfortunately, a large amount of LH 2 cold energy is not utilized but rather dissipated to the environment through HEX-1, which decreases the overall efficiency of the LH 2 supply chain.
In order to recover the energy spent for liquefaction, a kind of on-board liquid hydrogen cold energy utilization system is proposed, as shown in Figure 3. Different from the original LH 2 system, the LH 2 from the tank firstly passes through HEX-1 to cool the inlet air of the air compressor, rather than the ambient air, and thus reduces the power consumption of the compressor. In addition, the load of the intercooler is also reduced, which is beneficial, owing to the size reduction of intercooler. H 2 also needs to pass through HEX-2 to be further heated by the coolant. This process cools the coolant and thus the water pump power and the radiator fan power can be reduced. In other words, HEX-2 serves as a radiator for the accessories cooling system. However, the cold energy transferred to the system may exceed the cooling demand under low ambient temperature. Therefore, an electric heater is used to maintain the coolant temperature, which eventually keeps the temperature of the fuel cell stack inlet of H 2 and air within proper range.  In order to recover the energy spent for liquefaction, a kind of on-board liquid hydrogen cold energy utilization system is proposed, as shown in Figure 3. Different from the original LH2 system, the LH2 from the tank firstly passes through HEX-1 to cool the inlet air of the air compressor, rather than the ambient air, and thus reduces the power consumption of the compressor. In addition, the load of the intercooler is also reduced, which is beneficial, owing to the size reduction of intercooler. H2 also needs to pass through HEX-2 to be further heated by the coolant. This process cools the coolant and thus the water pump power and the radiator fan power can be reduced. In other words, HEX-2 serves as a radiator for the accessories cooling system. However, the cold energy transferred to the system may exceed the cooling demand under low ambient temperature. Therefore, an electric heater is used to maintain the coolant temperature, which eventually keeps the temperature of the fuel cell stack inlet of H2 and air within proper range.  In order to recover the energy spent for liquefaction, a kind of on-board liquid hydrogen cold energy utilization system is proposed, as shown in Figure 3. Different from the original LH2 system, the LH2 from the tank firstly passes through HEX-1 to cool the inlet air of the air compressor, rather than the ambient air, and thus reduces the power consumption of the compressor. In addition, the load of the intercooler is also reduced, which is beneficial, owing to the size reduction of intercooler. H2 also needs to pass through HEX-2 to be further heated by the coolant. This process cools the coolant and thus the water pump power and the radiator fan power can be reduced. In other words, HEX-2 serves as a radiator for the accessories cooling system. However, the cold energy transferred to the system may exceed the cooling demand under low ambient temperature. Therefore, an electric heater is used to maintain the coolant temperature, which eventually keeps the temperature of the fuel cell stack inlet of H2 and air within proper range.

System Model
To analyze the cold energy and the cooling demand under different working condi-

System Model
To analyze the cold energy and the cooling demand under different working conditions and ambient temperature, a zero-dimensional model was established based on AMESim (Figure 4), which includes four parts: fuel cell stack, H 2 supply subsystem, air supply subsystem, and the accessories cooling subsystem. AMESim is an integrated, scalable system simulation platform and consists of multi-physics libraries, which make it suitable for the modeling of thermal management systems by simulating heat transfer between solids, liquids, and gas, as well as through phase change phenomena [14]. The four subsystems are detailed as follows:

System Model
To analyze the cold energy and the cooling demand under different working conditions and ambient temperature, a zero-dimensional model was established based on AMESim (Figure 4), which includes four parts: fuel cell stack, H2 supply subsystem, air supply subsystem, and the accessories cooling subsystem. AMESim is an integrated, scalable system simulation platform and consists of multi-physics libraries, which make it suitable for the modeling of thermal management systems by simulating heat transfer between solids, liquids, and gas, as well as through phase change phenomena [14]. The four subsystems are detailed as follows:

Fuel Cell Stack Model
In this study, a zero-dimensional fuel cell stack model was developed to determine the electric voltage and output power under different current density. The polarization curve was obtained from the following equation: V nernst = 1.23 V is Nernst theoretical voltage, V act is activation polarization, V conc is concentration polarization, and V ohmic is ohmic polarization.
Equation (1) is calibrated using experimental data (as shown in Figure 5) and embedded in the AMESim fuel cell module. Therefore, the current and voltage under different fuel cell stack loads can be calculated, which is crucial to determine the maximum LH 2 cold energy. Vnernst = 1.23 V is Nernst theoretical voltage, Vact is activation polarization, Vconc is concentration polarization, and Vohmic is ohmic polarization.
Equation (1) is calibrated using experimental data (as shown in Figure 5) and embedded in the AMESim fuel cell module. Therefore, the current and voltage under different fuel cell stack loads can be calculated, which is crucial to determine the maximum LH2 cold energy.

H2 Supply Subsystem
H2 flow rate was determined by the fuel cell stack load and was calculated as follows: where Ncell is the number of cells in the stack, I is the current of the fuel cell stack, 2 is relative molecular mass of H2, 2 = 1.05 is H2 stoichiometric ratio, and F = 96485 C/mol is Faraday's constant.
The low temperature H2 sequentially passes through HEX-1 and HEX-2 and exchanges heat with the inlet air of the stack and the coolant of the accessories cooling system.
As for HEX-1 and HEX-2, they were simulated by the convective heat exchange modules in AMESim, and the performance of heat exchangers under different flow rates at room temperature was calibrated by experiments.

Air Supply Subsystem
Air flow rate was also determined by the stack load and was calculated as follows: where 2 is relative molecular mass of O2, is air stoichiometric ratio, and = 21% is the mass fraction of O2 in air.
varies with fuel cell load (as shown in Figure 6).

H 2 Supply Subsystem
H 2 flow rate was determined by the fuel cell stack load and was calculated as follows: .
where N cell is the number of cells in the stack, I is the current of the fuel cell stack, M H 2 is relative molecular mass of H 2 , S H 2 = 1.05 is H 2 stoichiometric ratio, and F = 96,485 C/mol is Faraday's constant. The low temperature H 2 sequentially passes through HEX-1 and HEX-2 and exchanges heat with the inlet air of the stack and the coolant of the accessories cooling system.
As for HEX-1 and HEX-2, they were simulated by the convective heat exchange modules in AMESim, and the performance of heat exchangers under different flow rates at room temperature was calibrated by experiments.

Air Supply Subsystem
Air flow rate was also determined by the stack load and was calculated as follows: where M O 2 is relative molecular mass of O 2 , S air is air stoichiometric ratio, and ω = 21% is the mass fraction of O 2 in air. S air varies with fuel cell load (as shown in Figure 6). Under light load (<50%), the stoichiometric ratio should be higher to ensure the basic flow rate and pressure. With the increase of load, the working condition of the fuel cell stack becomes stable, which means that lower stoichiometric ratio could satisfy the requirements of stack. Consequently, S air decreases gradually and remains almost constant after reaching a proper value (about 1.6). The ambient air was firstly cooled by low temperature H 2 and then compressed by air compressor. The outlet pressure and isentropic efficiency of the air compressor were determined by the map of the compressor, which was tested at different, corrected rotary speeds and corrected air flow rates (as shown in Figure 7). becomes stable, which means that lower stoichiometric ratio could satisfy the requirements of stack. Consequently, decreases gradually and remains almost constant after reaching a proper value (about 1.6).
The ambient air was firstly cooled by low temperature H2 and then compressed by air compressor. The outlet pressure and isentropic efficiency of the air compressor were determined by the map of the compressor, which was tested at different, corrected rotary speeds and corrected air flow rates (as shown in Figure 7).

Accessories Cooling Subsystem
The accessories cooling subsystem is mainly used to take heat away from DC/DC, intercooler, and other heat generating accessories. The main components include the water pump, PTC heater, DC/DC, intercooler, HEX-2, and radiator. The water pump and radiator fan performance curves were curve-fitted with experiments. Figure 8 shows the heat exchange power of radiator at different coolant flow rates and air flow speeds (the temperature difference of the coolant and air is 25 °C ). In addition, the pump flow rate and fan speed are controlled by temperature feedback to ensure that the coolant temperature kept in a proper range. becomes stable, which means that lower stoichiometric ratio could satisfy the requirements of stack. Consequently, decreases gradually and remains almost constant after reaching a proper value (about 1.6).
The ambient air was firstly cooled by low temperature H2 and then compressed by air compressor. The outlet pressure and isentropic efficiency of the air compressor were determined by the map of the compressor, which was tested at different, corrected rotary speeds and corrected air flow rates (as shown in Figure 7).

Accessories Cooling Subsystem
The accessories cooling subsystem is mainly used to take heat away from DC/DC, intercooler, and other heat generating accessories. The main components include the water pump, PTC heater, DC/DC, intercooler, HEX-2, and radiator. The water pump and radiator fan performance curves were curve-fitted with experiments. Figure 8 shows the heat exchange power of radiator at different coolant flow rates and air flow speeds (the temperature difference of the coolant and air is 25 °C ). In addition, the pump flow rate and fan speed are controlled by temperature feedback to ensure that the coolant temperature kept in a proper range.

Accessories Cooling Subsystem
The accessories cooling subsystem is mainly used to take heat away from DC/DC, intercooler, and other heat generating accessories. The main components include the water pump, PTC heater, DC/DC, intercooler, HEX-2, and radiator. The water pump and radiator fan performance curves were curve-fitted with experiments. Figure 8

Cold Energy Utilization Ratio Analysis
To evaluate the utilization of cold energy under different ambient temperatures and fuel cell stack loads, an index called cold energy utilization ratio was proposed and defined as follows: where Eused is the cold energy which is actually used through this system, and 2 is the maximum cold energy of LH2, which equals the LH2 enthalpy change from the LH2 tank (20K) to the inlet of the fuel cell stack (323K). Eused contains two parts: where Ecomp is the LH2 cold energy used for cooling the compressor inlet air and Ecoolant is the LH2 cold energy used for cooling the coolant. To be more specific, Ecomp is calculated as follows: where 2 is the mass of liquid hydrogen flow, Δh1 is the enthalpy change of H2 in HEX-1, and Edemand is the actual cooling demand of the air, which means that, if 2 Δh1 exceeds the actual cooling demand, the excessive part of cold energy would not be included in Ecomp. In fact, the excessive part would mean that the outlet air temperature of the compressor is lower than the lowest limiting value. Therefore, the air was heated rather than cooled in the intercooler. Through this process, the excessive cold energy in the HEX-1 is finally exchanged with coolant. Consequently, Ecoolant was calculated as follows: where Δh2 is the enthalpy change of H2 in HEX-2, Eextra is the excessive part of the cold energy exchanged in the HEX-1, which exceeds the cooling demand of air, and Eheater is the heater power.

Cold Energy Utilization Ratio Analysis
To evaluate the utilization of cold energy under different ambient temperatures and fuel cell stack loads, an index called cold energy utilization ratio was proposed and defined as follows: where E used is the cold energy which is actually used through this system, and E LH 2 is the maximum cold energy of LH 2 , which equals the LH 2 enthalpy change from the LH 2 tank (20K) to the inlet of the fuel cell stack (323K). E used contains two parts: where E comp is the LH 2 cold energy used for cooling the compressor inlet air and E coolant is the LH 2 cold energy used for cooling the coolant. To be more specific, E comp is calculated as follows: where m LH 2 is the mass of liquid hydrogen flow, ∆h 1 is the enthalpy change of H 2 in HEX-1, and E demand is the actual cooling demand of the air, which means that, if m LH 2 ∆h 1 exceeds the actual cooling demand, the excessive part of cold energy would not be included in E comp . In fact, the excessive part would mean that the outlet air temperature of the compressor is lower than the lowest limiting value. Therefore, the air was heated rather than cooled in the intercooler. Through this process, the excessive cold energy in the HEX-1 is finally exchanged with coolant. Consequently, E coolant was calculated as follows: where ∆h 2 is the enthalpy change of H 2 in HEX-2, E extra is the excessive part of the cold energy exchanged in the HEX-1, which exceeds the cooling demand of air, and E heater is the heater power.

Parasitic Power Analysis
In order to show the effect of LH 2 cold energy more intuitively, the parasitic power of the original system and the cold energy utilization system are calculated and compared. The total parasitic power P total includes four parts: P total = P comp + P heater + P f an + P pump (9) where P comp is air compressor power, P heater is heater power, P fan is radiator fan power, and P pump is water pump power.

Results and Discussion
The simulation results achieved under a steady state, including the cold energy utilization ratio and parasitic power savings, were analyzed to evaluate the performance of the LH 2 cold energy utilization system. Some important parameters and boundary conditions are shown in Table 1. In the HEX-1 inlet, the H 2 temperature is assumed to be −220 • C, to simulate the pipe heat loss between the LH 2 tank and vaporizer.  Figure 9 demonstrates the LH 2 cold energy utilization ratio under different ambient temperatures (including −30 • C, −10 • C, 20 • C, and 40 • C) and fuel cell stack loads (25~100%). At a low temperature (<−10 • C, as shown in Figure 9a,b), the cold energy is mainly used for cooling the coolant (accounting for at least 62% of the total utilized cold energy). In addition, the total cold energy utilization ratio is lower than 50% at light load (<50%). The reason for this is that the cooling demand of the system, especially the air pre-cooling demand, is near zero or even negative, due to the low inlet air temperature. Therefore, a part of the cold energy exchanged in HEX-1 and HEX-2 is not actually utilized. While at room temperature and higher (as shown in Figure 9c,d), the cold energy utilization ratio can maintain a high level (about 82%) under different loads, due to the increase of the total cooling demand. Moreover, and different from the results at low temperature, the air pre-cooling part accounts for about 85% of the total utilized cold energy, which indicates that a large part of cold energy is exchanged in HEX-1 and is entirely used for air pre-cooling. Figure 10a demonstrates the change of η with an ambient temperature and fuel cell stack load. The results show that cold energy utilization ratio increases with temperature and load. Figure 10b shows the contour map of η. It can be seen that the high utilization ratio zone occupies the main part on the whole working range. Specifically, η could reach 80% when the ambient temperature was above −10 • C and could keep above 80% in the whole load range when the temperature was above 20 • C, which indicates that the majority of LH 2 cold energy could be utilized through this system.  Figure 10a demonstrates the change of η with an ambient temperature and fuel cell stack load. The results show that cold energy utilization ratio increases with temperature and load. Figure 10b shows the contour map of η. It can be seen that the high utilization ratio zone occupies the main part on the whole working range. Specifically, η could reach 80% when the ambient temperature was above −10 °C and could keep above 80% in the whole load range when the temperature was above 20 °C , which indicates that the majority of LH2 cold energy could be utilized through this system.

Parasitic Power Saving Results
Compared to the original system without cold energy utilization, the parasitic power under different ambient temperatures (including −30 °C , −10 °C , 20 °C , and 40 °C ) and fuel cell stack loads (25~100%) are shown in Figure 11.

Parasitic Power Saving Results
Compared to the original system without cold energy utilization, the parasitic power under different ambient temperatures (including −30 • C, −10 • C, 20 • C, and 40 • C) and fuel cell stack loads (25~100%) are shown in Figure 11.
(a) (b) Figure 10. LH2 cold energy utilization ratio results: (a) Cold energy utilization ratio as a function of ambient temperature and FC load; (b) Cold energy utilization system contour map.

Parasitic Power Saving Results
Compared to the original system without cold energy utilization, the parasitic power under different ambient temperatures (including −30 °C , −10 °C , 20 °C , and 40 °C ) and fuel cell stack loads (25~100%) are shown in Figure 11.   At each stack load, the histogram on the left side (labeled as 'New') represents the parasitic power consumption of the LH 2 cold energy utilization system, and the histogram on the right side (labeled as 'Original') represents the parasitic power consumption of the original system. As shown in Figure 11a,b, it can be seen that, under low temperature (<−10 • C) and light load (<50%), the power consumption of the heater (yellow column) of the original system accounts for a large proportion (up to 67% of P total ), indicating that the system does not have a suitable cooling demand and needs additional heat generation to meet thermal balance. Therefore, even though the cold energy utilization reduces air compressor power (red column), the reduction is limited compared to the increase in heater power, meaning that the total power consumption of the system may increase as a result. While at room temperature and higher (as shown in Figure 11c,d), the air compressor power increases and the heater stops working. Therefore, the use of cold energy can significantly reduce the air compressor power by decreasing the inlet temperature of compressor, which leads to obvious power saving (up to 1.4 kW), especially at a high load. As for the power of the water pump and radiator fan (green and blue columns), they account for a small part of the total power consumption. This is mainly because the maximum power consumption of the water pump and radiator fan is much smaller compared to the compressor power (about 5%). Thus, the power saving of the water pump and radiator fan is not significant, except under 40 • C and a 100% load. Figure 12a demonstrates the change of saving power with ambient temperature and a fuel cell stack load. The red plane is the 0-saving power base plane. The LH 2 cold energy utilization system can realize power saving except under low temperature and light load. and the saving power increases with temperature and load. The maximum saving power can achieve 1.8 kW (40 • C, 100% load), which is about 15% of the total parasitic power of the original system without cold energy utilization. Through a comparison of the saving power curve and 0-saving power base plane, the system can be divided into two states-a power saving state and a non-power saving state (as shown in Figure 12b). It can be seen that the load range corresponding to power saving increases with the temperature. The system is possible to realize power saving when the ambient temperature is above −25 • C and could save power in the whole load range when the temperature is above 16 • C. In addition, the heat load of the intercooler can also be reduced due to the temperature decrease of the compressed air. The maximum saving heat load is about 4.5 kW, which is about 50% of the intercooler heat load in the original system. nificantly reduce the air compressor power by decreasing the inlet temperature of compressor, which leads to obvious power saving (up to 1.4 kW), especially at a high load. As for the power of the water pump and radiator fan (green and blue columns), they account for a small part of the total power consumption. This is mainly because the maximum power consumption of the water pump and radiator fan is much smaller compared to the compressor power (about 5%). Thus, the power saving of the water pump and radiator fan is not significant, except under 40 °C and a 100% load. Figure 12a demonstrates the change of saving power with ambient temperature and a fuel cell stack load. The red plane is the 0-saving power base plane. The LH2 cold energy utilization system can realize power saving except under low temperature and light load. and the saving power increases with temperature and load. The maximum saving power can achieve 1.8 kW (40 °C , 100% load), which is about 15% of the total parasitic power of the original system without cold energy utilization. Through a comparison of the saving power curve and 0-saving power base plane, the system can be divided into two statesa power saving state and a non-power saving state (as shown in Figure 12b). It can be seen that the load range corresponding to power saving increases with the temperature. The system is possible to realize power saving when the ambient temperature is above −25 °C and could save power in the whole load range when the temperature is above 16 °C . In addition, the heat load of the intercooler can also be reduced due to the temperature decrease of the compressed air. The maximum saving heat load is about 4.5 kW, which is about 50% of the intercooler heat load in the original system.

Conclusions
A kind of on-board liquid hydrogen cold energy utilization system is proposed and analyzed. By using two heat exchangers, the cold energy of LH 2 is utilized for cooling the inlet air of the compressor and the coolant of the accessories cooling system sequentially. A zero-dimensional model was established to analyze the performance of the system. The simulation results show that the cold energy utilization ratio can keep at a high level (above 80%), except under extremely low temperatures and light fuel cell stack load. Compared to the original LH 2 system without cold energy utilization, the new system could realize power saving when the ambient temperature was above −25 • C, and the maximum saving power achieved was 1.8 kW, which is about 15% of the total parasitic power. In addition, the intercooler heat load can also be reduced, which is beneficial as it reduces the size of the intercooler.
The on-board LH 2 cold energy utilization improves the overall efficiency of LH 2 and saves the system parasitic power consumption of heavy-duty fuel cell hybrid truck, which makes it more competitive as a fuel source. However, the analysis of the system is still preliminary, and the optimization of cold energy distribution between two heat exchangers needs to be simulated and verified. Other arrangements should be compared to explore the change of the inlet and outlet temperature of the heat exchanger and the impact on system's performance. Furthermore, the detailed control strategy of the system under different dynamic cycles is another important aspect in future research. Acknowledgments: This research was supported by Beijing Institute of Aerospace Testing Technology, Beijing SinoHytec Co., Ltd. and Beiqi Foton Motor Co., Ltd.

Conflicts of Interest:
The authors declare no conflict of interest. The funders had no role in the design of the study; in the collection, analyses, or interpretation of data; in the writing of the manuscript, or in the decision to publish the results.