Conceptual Design of a Compact Divertor Heat Load Simulation Device: HIT-PSI

: Linear plasma devices have been increasingly applied in investigating plasma–surface interaction (PSI) processes and divertor/scraped-off-layer (D/SOL) physics because of their economy, ﬂexibility, and expandability. However, only a few existing linear plasma devices are able to obtain high heat and particle ﬂuxes. In this work, we report a compact superconducting linear device, with its scientiﬁc goals and speciﬁc design methods, at Harbin Institute of Technology (HIT), HIT-PSI, capable of implementing an extreme plasma environment with beams of a long discharge pulse, as well as high heat and particle ﬂuxes in the future fusion reactor regime of ITER/CFETR-like parameters. A ﬁve-coil integrated superconducting magnet is designed to generate a >2.0 Tesla steady-state magnetic ﬁeld for conﬁning a long pulse plasma beam with a density of >10 20 m − 3 produced by a cascaded arc plasma source. With a pump set of 2500 L/s and a water-cooled target system with bias voltage, it is expected to obtain high-density and low-temperature plasma beams with a heat ﬂux of over 10 MW/m 2 . Subsystems of the platform, including the plasma source, superconducting magnets, vacuum system, and target holder system, are described in detail. In addition, the function and performance of the platform are numerically simulated and represented by SOLPS-ITER code to predict the laboratory simulation results.


Introduction
In tokamak operations, plasma-surface interaction (PSI) processes under extreme conditions have profound impacts on operational safety, performance metrics, and economical efficiency of fusion reactors, and have become one of the primary foci of fusion studies [1][2][3]. High heat and particle fluxes reaching plasma-facing components (PFCs) will cause erosion and tritium retention of materials [4]. Therefore, understanding and exploring the PSI mechanism is crucial to the realization of controlled nuclear fusion.
However, divertors in future fusion reactors such as ITER and CFETR are subject to extreme long-pulse high heat/particle fluxes, far beyond the parameters of existing tokamaks [5,6]. The performance of PFCs under such high-parameter plasma bombardments is thus an unknown territory. Various lab simulation devices for divertor plasmas have been developed for studying PSIs. Among them, linear plasma devices are the most widely adopted worldwide due to their economy, flexibility, and expandability, as well as their advantages as diagnostic test platforms. For example, a steady-state linear plasma device of PISCES-B is capable of testing radioactive and toxic materials such as Be [7,8]; another divertor simulator facility, NAGDIS-II, is applied in high-density plasma detachment studies [9]; and a device at Sichuan University with similar functions, SCU-PSI, is applied in PSI investigations of liquid materials [10,11]. The above-mentioned and many more established linear plasma devices have greatly advanced PSI research, along with diagnostic techniques, plasma sources, and plasma physics of low-temperature plasma [12][13][14][15][16][17]. There are

•
To investigate strongly coupled PSI regimes under high fluxes close to extreme firstwall plasma conditions similar to that of ITER-like reactors; • To examine the effects of chemistry and atomic physics in such boundary plasmas with high densities and low temperatures; • To explore low-temperature plasma diagnostic technologies under the D-SOL plasma and magnetic field conditions; • To develop high-parameter plasma source technologies in a strong magnetic field environment.
HIT-PSI is schematically depicted in Figure 1. It mainly consists of a cascaded arc plasma source, a superconducting magnet, a target holder, as well as a vacuum, and other related auxiliary subsystems. The design specifications of HIT-PSI are listed in Table 1, where plasma parameters of serval typical linear plasma simulator devices and the ITERlike divertor are also represented for comparison.

Plasma Source
Both RF and cascaded arc sources have been experimentally demonstrated to satisfy the demand for the plasma source of a linear plasma device with ITER-like high heat flux by MPEX and Magnum-PSI [20,21]. However, the RF sources are typically of a lower density, and thus other assisting heating means are necessary to achieve a high plasma temperature. It is then a great technical challenge with notable cost. By contrast, cascaded arc sources are more advantageous since they can generate higher-density plasmas with a temperature of up to several eVs without extra heating. Consequently, we applied cascaded arc sources in HIT-PSI.
The cascaded arc plasma source was invented in the 1960s by Maecker [25] and first constructed and optimized with three channels in 2009 [26] at Eindhoven University of Technology. It has also been experimentally explored at Harbin Institute of Technology for years [27]. The three-channel cascaded arc plasma source and its anode flange are shown in Figure 2. Three to five cascade plates made of pure copper are sandwiched between the anode flange and separated by Boron nitride gaskets, with water cooling. Molybdenum rings are inserted into the cascade plates to face the plasma. Three cathode pins made of tungsten are put on top. For argon gas discharge with no magnetic field, each current channel can reach 160 A, and the plasma density may exceed 10 19 m −3 .  Multiple channels of the cascaded arc plasma cannot increase the plasma beam density, especially when a strong magnetic field exists to limit the mix of separated channel beams, resulting in an uneven plasma density. Therefore, either a single-channel or a three-channel cascaded arc plasma source has been applied to meet the requirement of various features of the plasma beam in different operation scenarios.
The water-cooling architecture of cascade plates is a key factor for the long-term steady-state operation of the arc source. An optimized waterway designed by COMSOL Multiphysics is shown in Figure 3, which is efficient in terms of heat dissipation and water pressure reduction. Complex waterway designs can be achieved to maximize water cooling efficiency by diffusion welding. Multiple channels of the cascaded arc plasma cannot increase the plasma beam density, especially when a strong magnetic field exists to limit the mix of separated channel beams, resulting in an uneven plasma density. Therefore, either a single-channel or a three-channel cascaded arc plasma source has been applied to meet the requirement of various features of the plasma beam in different operation scenarios.
The water-cooling architecture of cascade plates is a key factor for the long-term steady-state operation of the arc source. An optimized waterway designed by COMSOL Multiphysics is shown in Figure 3, which is efficient in terms of heat dissipation and water sity, especially when a strong magnetic field exists to limit the mix of separated channel beams, resulting in an uneven plasma density. Therefore, either a single-channel or a three-channel cascaded arc plasma source has been applied to meet the requirement of various features of the plasma beam in different operation scenarios.
The water-cooling architecture of cascade plates is a key factor for the long-term steady-state operation of the arc source. An optimized waterway designed by COMSOL Multiphysics is shown in Figure 3, which is efficient in terms of heat dissipation and water pressure reduction. Complex waterway designs can be achieved to maximize water cooling efficiency by diffusion welding.

Superconducting Magnets
In a linear plasma device for PSI research, the role of the magnetic field is to confine the radial diffusion of the plasma beam and to limit the radius of the sputtered particle rotation to smaller than the re-deposited material sample. Meanwhile, previous experimental results of Magnum-PSI showed that the application of a strong magnetic field could improve the performance of the arc plasma source, where a higher ionization rate and a more effective rise of the plasma density and temperature approaching the target plate can be achieved [23,28]. When the confinement magnetic field of the source reaches

Superconducting Magnets
In a linear plasma device for PSI research, the role of the magnetic field is to confine the radial diffusion of the plasma beam and to limit the radius of the sputtered particle rotation to smaller than the re-deposited material sample. Meanwhile, previous experimental results of Magnum-PSI showed that the application of a strong magnetic field could improve the performance of the arc plasma source, where a higher ionization rate and a more effective rise of the plasma density and temperature approaching the target plate can be achieved [23,28]. When the confinement magnetic field of the source reaches a~Tesla level, the heat flux can reach~10 MW/m 2 . Thus, a superconducting magnet subsystem to generate a steady-state strong magnetic field is essential.
The construction of superconducting magnets may take a major share of the budget. Therefore, the design should be well balanced among physical needs, engineering challenges, operating costs, and budget allowed. The design parameters then have to mostly meet the following needs: • Safety, which always comes first, including personnel and operational safety needs; • An axial magnetic field of >2.0 T with great homogeneity; • More than 1000 mm axial distance of beam transmission, for future experimental research with a radial size as large as possible, enough for the vacuum chamber to accommodate the beam; • Radial windows left for pumping and diagnostic needs; • A fast excitation for experimental flexibility; • Also, a low cost for operation, maintenance, and construction.
Taking the above factors into consideration, the superconducting magnet design, shown in Figure 4, adopts an integrated system immersed in a closed cryostat containing liquid helium and directly cooled by a cryocooler to form a zero-boil-off system. Only a tiny amount of liquid helium is needed to keep the steady-state operation of the magnets. The main body of a superconducting magnet is shown in Figure 5, with an inner diameter of 450 mm, a total length of 1804.4 mm, and a total weight of 348.7 kg. In addition, eight radially distributed room temperature ports with a diameter of 167.6 mm for each are reserved for diagnostics and vacuum pump connection.
shown in Figure 4, adopts an integrated system immersed in a closed cryostat containing liquid helium and directly cooled by a cryocooler to form a zero-boil-off system. Only a tiny amount of liquid helium is needed to keep the steady-state operation of the magnets. The main body of a superconducting magnet is shown in Figure 5, with an inner diameter of 450 mm, a total length of 1804.4 mm, and a total weight of 348.7 kg. In addition, eight radially distributed room temperature ports with a diameter of 167.6 mm for each are reserved for diagnostics and vacuum pump connection.  shown in Figure 4, adopts an integrated system immersed in a closed cryostat containing liquid helium and directly cooled by a cryocooler to form a zero-boil-off system. Only a tiny amount of liquid helium is needed to keep the steady-state operation of the magnets. The main body of a superconducting magnet is shown in Figure 5, with an inner diameter of 450 mm, a total length of 1804.4 mm, and a total weight of 348.7 kg. In addition, eight radially distributed room temperature ports with a diameter of 167.6 mm for each are reserved for diagnostics and vacuum pump connection.  The major parameters of the superconducting magnet subsystem are listed in Table 2. A total of five solenoid coils are utilized in the superconducting magnet subsystem to ensure the preferred axial homogeneity of the magnetic field with a possibility of flexible modification.  Table 3 is for the coil parameters. The magnetic field distribution generated by the maximum operating current of 275 A is shown in Figure 6 by Comsol 2D axisymmetric modeling. Coils 1 and 5, symmetrically distributed on both sides of Coil 3, have the same parameters. So do Coils 2 and 4. Copper stabilized (Cu/Sc:4) NbTi conductor lines of totally 23.77 km, with an insulated rectangular cross-section of 1.65 × 1.0 mm 2 and an insulating layer of 0.04 mm, are adopted. Due to the space left for room temperature bores between Coil Pairs 2/4 and 1/5, Coils 1 and 5 have more layers to improve homogeneity. Both the source and the target are placed near room temperature bores for easy observation and diagnosis. The plasma density of the beam generated by the cascaded arc plasma source exhibits a Gaussian distribution, and the radial full width at the half maximum (FWHM) of the plasma density is less than 50 mm due to the confinement of the strong magnetic field [19]. Moreover, the magnetic field distribution in the main plasma transmission region (enclosed in Figure 6 by red dots), with a length of 1300 mm along the axis and a radius of 50 mm, is illustrated in Figure 7. The average magnetic intensity in this region is 2.33 T, with a field uniformity of ±9.7%.   Furthermore, Table 4 lists the inductance matrix of five coils. To obtain better exper imental adaptability, the ramp time of the coil current needs to be minimized. For th excitation voltage distribution of 30.4%/8.1%/20.0%/8.1%/30.4%, the ramp-up time of 32.  Furthermore, Table 4 lists the inductance matrix of five coils. To obtain better experimental adaptability, the ramp time of the coil current needs to be minimized. For the excitation voltage distribution of 30.4%/8.1%/20.0%/8.1%/30.4%, the ramp-up time of 32.7 min at 5 volts and 54.5 min at 3 volts is aimed to reduce impacts while still meeting ade- Furthermore, Table 4 lists the inductance matrix of five coils. To obtain better experimental adaptability, the ramp time of the coil current needs to be minimized. For the excitation voltage distribution of 30.4%/8.1%/20.0%/8.1%/30.4%, the ramp-up time of 32.7 min at 5 volts and 54.5 min at 3 volts is aimed to reduce impacts while still meeting adequate technical standards. The cryogenic cooling arrangements, including current leads, cryocooler, gas supplement valves, liquid helium injection ports, auxiliary helium interfaces, pressure measurement interfaces, bursting membranes, exhaust valves, and coil protection circuit accessories, are all integrated into the service tower (Figure 4g This superconducting magnet subsystem with a lot of radial windows is a new challenge for design and construction. Extra attention to its stability and safety is particularly necessary. The first and most needed task is to control the occurrence of quench. There are many possible causes for quench, and for this integrated design of a multi-coil superconducting magnet, an enormous electromagnetic force exists between the coils. The force may cause coil movements, resulting in asymmetrical twists to symmetrically designed coils, and thus result in catastrophic repercussions. The axial and radial Lorentz force distributions between different coils are shown in Figure 8. This superconducting magnet subsystem with a lot of radial windows is a new challenge for design and construction. Extra attention to its stability and safety is particularly necessary. The first and most needed task is to control the occurrence of quench. There are many possible causes for quench, and for this integrated design of a multi-coil superconducting magnet, an enormous electromagnetic force exists between the coils. The force may cause coil movements, resulting in asymmetrical twists to symmetrically designed coils, and thus result in catastrophic repercussions. The axial and radial Lorentz force distributions between different coils are shown in Figure 8.  There are 15 resistors placed outside the heat-insulating theater in three groups to provide quench protection. The quench protection circuit diagram is depicted in Figure 9. As quench occurs, the energy is lost to resistance, converting to heat and releasing immediately. As seen in Figure 10, the current drops rapidly within 6 s after the quench occurs. More detailed information on quench protection simulation and experimental test results  There are 15 resistors placed outside the heat-insulating theater in three groups to provide quench protection. The quench protection circuit diagram is depicted in Figure 9. As quench occurs, the energy is lost to resistance, converting to heat and releasing immediately. As seen in Figure 10, the current drops rapidly within 6 s after the quench occurs. More detailed information on quench protection simulation and experimental test results will be presented in future works.  The magnetic stray field is shielded by external iron walls. The 5.5 cm-thick iron walls are constructed outside the superconducting magnet. Following the shielding layer installation, the interior and exterior magnetic fields are shown in Figure 11. The stray magnetic field of less than 50 Gauss is detected at 2.3 m away from the magnet, which can meet the safety limits required [29].  The magnetic stray field is shielded by external iron walls. The 5.5 cm-thick iron walls are constructed outside the superconducting magnet. Following the shielding layer installation, the interior and exterior magnetic fields are shown in Figure 11. The stray magnetic field of less than 50 Gauss is detected at 2.3 m away from the magnet, which can meet the safety limits required [29]. The magnetic stray field is shielded by external iron walls. The 5.5 cm-thick iron walls are constructed outside the superconducting magnet. Following the shielding layer installation, the interior and exterior magnetic fields are shown in Figure 11. The stray magnetic field of less than 50 Gauss is detected at 2.3 m away from the magnet, which can meet the safety limits required [29].

Vacuum Subsystem
The diagram of the vacuum subsystem is isometrically given in Figure 12. The chamber and associated pipelines for vacuum and diagnosis are strictly constrained by the superconducting magnet. The inner diameter of the vacuum chamber is 350 mm. It features a water-cooled interlayer divided into four independent zones to protect the chamber from plasma bombardment and ensure no heat conduction to the magnet. In addition, 8 pipes are distributed radially with an inner diameter of 150 mm.

Vacuum Subsystem
The diagram of the vacuum subsystem is isometrically given in Figure 12. The chamber and associated pipelines for vacuum and diagnosis are strictly constrained by the superconducting magnet. The inner diameter of the vacuum chamber is 350 mm. It features a water-cooled interlayer divided into four independent zones to protect the chamber from plasma bombardment and ensure no heat conduction to the magnet. In addition, 8 pipes are distributed radially with an inner diameter of 150 mm. Appl. Sci. 2022, 12, x FOR PEER REVIEW 10 of 17 Figure 11. Distribution of the stray magnetic field within 3 m radius from the magnet, with 100 Gausses of the stray field at 1.9 m and 50 Gausses of the stray field at 2.3 m.

Vacuum Subsystem
The diagram of the vacuum subsystem is isometrically given in Figure 12. The chamber and associated pipelines for vacuum and diagnosis are strictly constrained by the superconducting magnet. The inner diameter of the vacuum chamber is 350 mm. It features a water-cooled interlayer divided into four independent zones to protect the chamber from plasma bombardment and ensure no heat conduction to the magnet. In addition, 8 pipes are distributed radially with an inner diameter of 150 mm.  Since the cascaded arc plasma source has a low ionization rate, most inlet gas enters the vacuum chamber as neutral particles. As a result, it is desirable to lower the neutral pressure because too much neutral gas may cause inelastic collisions, such as ionization and recombination, which directly reduces heat and particle fluxes of the beam. Therefore, a set of a screw pump of 150 L/s and two Roots pumps of 300 L/s and 2500 L/s is applied. With a 3 L/min argon inflow, the neutral pressure of the chamber can be controlled below 10 Pa. Meanwhile, two butterfly valves with adjustable opening and closing angles are installed to allow flexible adjustment of the pumping rate for the front and back parts of the chamber, respectively.

Target Holder Subsystem
The target subsystem is designed to accomplish the following goals:

•
To be combined with the target probe design for measurements of the heat load flux; • To complete tests for different sizes and shapes of materials; • To apply proper voltage to the sample for various incident ion energy regulations; • To realize plasma-material interaction experiments with different beam incident angles; • To achieve effective heat dissipation for long-duration experimental tests; A schematic diagram of the target holder is shown in Figure 13. The front of the target is a molybdenum baffle attached to a copper cooling plate with ceramic screws. The hole in the center is for the sample exposure or target probe placement. The sample to be analyzed is placed behind the molybdenum baffle. Both the ceramic holder and the molybdenum baffle may be replaced to accommodate the varying sizes and shapes of the samples. These components are mounted on a copper base with water cooling. The copper base is isolated from the rear flange and front molybdenum baffle to allow it to link to a DC power source for bias, along with the sample.
Since the cascaded arc plasma source has a low ionization rate, most inlet gas enters the vacuum chamber as neutral particles. As a result, it is desirable to lower the neutral pressure because too much neutral gas may cause inelastic collisions, such as ionization and recombination, which directly reduces heat and particle fluxes of the beam. Therefore, a set of a screw pump of 150 L/s and two Roots pumps of 300 L/s and 2500 L/s is applied. With a 3 L/min argon inflow, the neutral pressure of the chamber can be controlled below 10 Pa. Meanwhile, two butterfly valves with adjustable opening and closing angles are installed to allow flexible adjustment of the pumping rate for the front and back parts of the chamber, respectively.

Target Holder Subsystem
The target subsystem is designed to accomplish the following goals: • To be combined with the target probe design for measurements of the heat load flux; • To complete tests for different sizes and shapes of materials; • To apply proper voltage to the sample for various incident ion energy regulations; • To realize plasma-material interaction experiments with different beam incident angles; • To achieve effective heat dissipation for long-duration experimental tests; A schematic diagram of the target holder is shown in Figure 13. The front of the target is a molybdenum baffle attached to a copper cooling plate with ceramic screws. The hole in the center is for the sample exposure or target probe placement. The sample to be analyzed is placed behind the molybdenum baffle. Both the ceramic holder and the molybdenum baffle may be replaced to accommodate the varying sizes and shapes of the samples. These components are mounted on a copper base with water cooling. The copper base is isolated from the rear flange and front molybdenum baffle to allow it to link to a DC power source for bias, along with the sample. Sensors are installed between the molybdenum baffle and the sample to measure the temperature of the sample. The inlet and outlet water-cooling pipes are also with thermometers and flow meters, and the combination of the two can give the heat load density. The entire target part can be rotated to realize material testing with different incident angles. Sensors are installed between the molybdenum baffle and the sample to measure the temperature of the sample. The inlet and outlet water-cooling pipes are also with thermometers and flow meters, and the combination of the two can give the heat load density. The entire target part can be rotated to realize material testing with different incident angles.

Numerical Simulation Device Capability with SOLPS
The capacity of the device is simulated by SOLPS-ITER [30], which has been widely used in linear plasma device simulation [31][32][33][34]. SOLPS-ITER is a code package for tokamak edge plasmas simulations with two main parts, B2.5 for solving multi-fluid simulation with Braginskii equations and EIRENE for neutral particles and molecular ions transport simulation by Monte Carlo methods.
In our simulation, we applied a 2D cylindrical coordinate system (R, Z) with axial symmetry, and the corresponding mesh grid is shown in Figure 14. The lower line is the symmetry axis in a symmetrical boundary condition with zero particle density flux. The quasi-orthogonal mesh region with a high resolution denotes plasma, with grids determined by magnetic field lines axially (in blue). The boundary condition on the outermost line has a decay range of 0.5 cm. The front and rear end in the axial direction are the Bohm boundaries, and energy transmission factors for electrons and ions are 1.0 and 1.5, respectively. The green triangular mesh of a lower resolution is for the EIRENE, where the recycling rate at the two pumping surfaces (bold red lines) is 0.95, and the rest are wall boundaries. There is an open boundary at the target end (assuming Z = 0 at the source, here Z = 1.33 m). The drift effect is ignored, and Braginskii equations are solved only along the direction of the magnetic field. Two sets of anomalous transport coefficients: D ⊥ = 0.3 m 2 /s, χ e,i = 0.9 m 2 /s (Case 1) and D ⊥ = 1.0 m 2 /s, χ e,i = 2.0 m 2 /s (Case 2) are adopted, corresponding to strong and weak magnetic fields, respectively. Plasma parameters at the source location are shown in Figure 15a, which are obtained by adjusting the external particle source applied heating power to the source surface (Z = 0). Slight differences in the two cases are due to various grids corresponding to the magnetic fields generated by 275 A and 75 A coil currents.

Numerical Simulation Device Capability with SOLPS
The capacity of the device is simulated by SOLPS-ITER [30], which has been widely used in linear plasma device simulation [31][32][33][34]. SOLPS-ITER is a code package for tokamak edge plasmas simulations with two main parts, B2.5 for solving multi-fluid simulation with Braginskii equations and EIRENE for neutral particles and molecular ions transport simulation by Monte Carlo methods.
In our simulation, we applied a 2D cylindrical coordinate system (R, Z) with axial symmetry, and the corresponding mesh grid is shown in Figure 14. The lower line is the symmetry axis in a symmetrical boundary condition with zero particle density flux. The quasi-orthogonal mesh region with a high resolution denotes plasma, with grids determined by magnetic field lines axially (in blue). The boundary condition on the outermost line has a decay range of 0.5 cm. The front and rear end in the axial direction are the Bohm boundaries, and energy transmission factors for electrons and ions are 1.0 and 1.5, respectively. The green triangular mesh of a lower resolution is for the EIRENE, where the recycling rate at the two pumping surfaces (bold red lines) is 0.95, and the rest are wall boundaries. There is an open boundary at the target end (assuming Z = 0 at the source, here Z = 1.33 m). The drift effect is ignored, and Braginskii equations are solved only along the direction of the magnetic field. Two sets of anomalous transport coefficients: adopted, corresponding to strong and weak magnetic fields, respectively. Plasma parameters at the source location are shown in Figure 15a, which are obtained by adjusting the external particle source applied heating power to the source surface (Z = 0). Slight differences in the two cases are due to various grids corresponding to the magnetic fields generated by 275 A and 75 A coil currents.   Figure 15b, Figure 16 and Figure 17 show the simulation results of the two cases. It can be seen that the general features of the two cases are basically the same, with very similar radial distributions of the electron temperature at the target end. The plasma density drops faster after leaving the source surface in Case 2 than that in Case 1, due to the more significant radial diffusion coefficient in a weaker field. In addition, one can find  Figures 15b, 16 and 17 show the simulation results of the two cases. It can be seen that the general features of the two cases are basically the same, with very similar radial distributions of the electron temperature at the target end. The plasma density drops faster after leaving the source surface in Case 2 than that in Case 1, due to the more significant radial diffusion coefficient in a weaker field. In addition, one can find that when Z < 1.1 m, the electron temperature drops from 4 eV to 1 eV, accompanied by a gentle electron density bump. This region is called the 'recombination front [29]', where the temperature is between 1 eV to 5 eV, causing ionization to dominate and leading to an electron density increase, but then electron density starts to decrease due to energy relaxation between ions and electrons. When Z > 1.1 m, the electron temperature drops to~1 eV, and thus recombination is dominant, resulting in a significant electron density drop. In addition, due to the existence of the pumping surface, the neutral particle pressure does not increase obviously along the axial direction.     The heat flux of the plasma beam can be calculated by [20]: where T e = T i assumed, Y is the polytropic exponent (in the adiabatic approximation), m is the ion mass, Y sh is the sheath heat transmission coefficient, and E i (n eV) is the deuterium ionization potential. Intercepting radial plasma parameters at Z = 1.33 m, the heat flux can be calculated, as shown in Figure 18. It can be observed that more intensive heat flux on the target can be achieved with a stronger magnetic field (Case 1). The major contribution to the heat flux rise comes from the electron density at the target due to the weaker perpendicular transport reduced by the magnetic confinement. Note that though the heat flux calculated provides a reasonable reference, it is numerically simulated by the upstream plasma parameters only without the target boundary setting yet. The heat flux of the plasma beam can be calculated by [20]: where assumed, Υ is the polytropic exponent (in the adiabatic approximation), is the ion mass, Υ is the sheath heat transmission coefficient, and (n eV) is the deuterium ionization potential. Intercepting radial plasma parameters at Z = 1.33 m, the heat flux can be calculated, as shown in Figure 18. It can be observed that more intensive heat flux on the target can be achieved with a stronger magnetic field (Case 1). The major contribution to the heat flux rise comes from the electron density at the target due to the weaker perpendicular transport reduced by the magnetic confinement. Note that though the heat flux calculated provides a reasonable reference, it is numerically simulated by the upstream plasma parameters only without the target boundary setting yet.

Summary
The specific design of a new platform, HIT-PSI, at Harbin Institute of Technology for PSI experiments is presented. The device is to simulate the specific plasma environment equivalent to that in divertors of future fusion reactors such as ITER/CFETR and to study plasma-material interactions under high heat and high-density plasma beams, as well as

Summary
The specific design of a new platform, HIT-PSI, at Harbin Institute of Technology for PSI experiments is presented. The device is to simulate the specific plasma environment equivalent to that in divertors of future fusion reactors such as ITER/CFETR and to study plasma-material interactions under high heat and high-density plasma beams, as well as low-temperature plasma processes in the scrape-off layer.
The platform utilizes a five-coil superconducting magnet subsystem with eight roomtemperature holes to generate a magnetic field of 2.0 T or beyond to confine high-density plasma of >10 20 m −3 generated by a cascaded arc source. All parts of the platform have been processed, and the discharge for the first plasma will be carried out soon. Preliminary simulation results by SOLPS-ITER show that HIT-PSI can reach a heat flux of > 10 MW/m 2 , capable of experimentally simulating the divertor environment in the future fusion reactor regime.

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