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Science and Technology of Nuclear Installations
Volume 2018, Article ID 4163914, 8 pages
https://doi.org/10.1155/2018/4163914
Research Article

Moisture Transfer Model and Simulation for Dehumidification of HTGR Core

1Institute of Nuclear and New Energy Technology, Collaborative Innovation Center of Advanced Nuclear Energy Technology, Key Laboratory of Advanced Reactor Engineering and Safety of Ministry of Education, Tsinghua University, Beijing 100084, China
2Nuclear Power Institute of China, Chengdu 610231, China

Correspondence should be addressed to Huaqiang Yin; nc.ude.auhgnist@gnaiqauhniy

Received 6 June 2018; Accepted 25 July 2018; Published 5 August 2018

Academic Editor: Eugenijus Ušpuras

Copyright © 2018 Jun Li et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

Abstract

A large number of carbon materials are adopted in high-temperature gas-cooled reactor (HTGR). These carbon materials mainly include graphite IG-110 and boron-containing carbon material (BC), both of which are typical porous materials and normally absorb moisture. In order to inhibit the chemical corrosion reaction between core internals materials and moisture, the core needs to be strictly dehumidified before the reactor is put into operation. This paper mainly analyzed the moisture transfer mechanism in these carbon materials. Moisture transfer models were developed, and the dehumidification process of HTR-PM core was simulated. In addition, the influence of working temperature and system pressure on dehumidification was studied as well.

1. Introduction

Due to the excellent comprehensive performance of carbon materials, they have been extensively adopted in high-temperature gas-cooled reactor (HTGR), serving as structural material, fuel matrix material, etc. [13]. These carbon materials used in HTGR typically include isostatic pressure graphite IG-110 and boron-containing carbon material (BC) [4]. Graphite IG-110 mainly serves as fuel matrix material, neutron reflecting layer, and other reactor core internals, while for BC, since it contains boron, which has a big neutron absorption cross section, it is made into the shielding layer [5]. It has been reported that about 60 tons and 1000 tons of graphite have been applied in 10 MW high-temperature gas-cooled reactor (HTR-10) [6] and high-temperature gas-cooled reactor-pebblebed modules (HTR-PM) [7], respectively.

As porous material, carbon materials have numerous pore structures and large specific surface area. The pore structures and molecule groups attached on the surface of pores result in strong moisture absorption capacity [8, 9]. Also, other impurities, such as H2O, O2, and CO2, can be absorbed by carbon materials as well. These impurities will react with the carbon materials at high temperature, thus, weakening the material strength and decreasing the service life of HTGR [1013]. In addition, under some extreme nuclear accidents, e.g., air or water leakage accident, the corrosion can be even more serious [14, 15]. In order to attenuate the corrosion, the limited value of moisture content in the helium coolant of the primary circuit is set as 2 cm3/m3 [16]. Therefore, before power operation and test, the reactor internals and fuel balls need to be dehumidified to control the moisture content to a certain level.

The dehumidification system [17] of HTR-PM is shown in Figure 1. Firstly, the primary circuit is evacuated and then filled with coolant helium at pressure of 7 MPa. The circulated helium is driven by helium circulator, whose mechanical energy is transformed into heat of helium. Thus, the temperature of helium can be heated to 250°C. Due to the high temperature, moisture absorbed in the carbon internals of reactor core will be released and then carried away by flowing helium. The helium flow containing relatively high moisture content will flow out of internals and then be cooled to about 20°C in two water-helium coolers, so the water vapor will condense to liquid water which can be separated in gas-water separator. Finally, dry helium will return to the reactor core. This circulation of helium flow described above will gradually decrease the moisture content in the carbon internals. After being dehumidified for several dozens of days, the moisture content of reactor core will meet the design requirement.

Figure 1: Dehumidification system of HTR-PM.

Dehumidification process mainly includes moisture transfer in carbon materials, moisture transfer in helium flow, and the condensation and separation of moisture. During dehumidification and purification process of reactor core, mass transfer in carbon material is considered as the dominating factor. Thus, mass transfer behavior in these carbon materials is worth investigating.

In this paper, Section 2 will present the analysis on moisture transfer mechanism in carbon materials, and then mathematical models will be developed in Section 3. In Section 4, the simulation on dehumidification of HTR-PM will be introduced, and simulation result will be analyzed.

2. Moisture Transfer Mechanism

2.1. Mass and Heat Transfer

Dehumidification process of porous material involves both moisture mass transfer and heat transfer, the relationship of which can be described by Lewis Number Le:where α (m2/s) and D (m2/s) are heat diffusion coefficient and mass diffusion coefficient respectively.

While Le > 60, it is thought that the heat transfer is faster much more than mass transfer, so that it can be neglected in the analysis [18]. For graphite, the heat diffusion coefficient is about 1.07 × 10−4 m2/s, and mass diffusion coefficient ranges 10−7 ~ 10−6 m2/s. Thus, Le of graphite ranges 102 ~ 103, which means that the heat transfer can be neglected, so it is thought that the mass transfer takes place at constant temperature in analysis.

Considering the moisture in material is in gaseous state, the mass transfer mechanism of gas in porous material involves molecular diffusion and seepage flow.

2.2. Molecular Diffusion

Molecular diffusion is the result of molecular thermal motion and collision, the mass flux density J (kg·m−2·s−1) caused by which can be described by Fick’s law:where ρ (kg/m3) is moisture concentration and De (m2/s) is effective diffusion coefficient. De is influenced by diffusion type, gas component, porosity of material and tortuosity of pore, etc. De can be expressed aswhere (m2/s) is the gas diffusion coefficient. is effective porosity of material, which is equal to open porosity in general. τ is tortuosity of pore, which is defined as the ratio of the actual length to the apparent length of pore. In addition, the tortuosity is in reciprocal relationship to the effective porosity; thus, relation has been adopted to the analysis of graphite [19, 20]. Table 1 summarizes the expressions of according to diffusion type and gas component.

Table 1: Expressions of according to diffusion type and gas component.

In Table 1, P (Pa) is the gas pressure, T (K) is the temperature, and R is gas constant which is 8.314 J/(mol·K) in general. (g/mol) and (g/mol) are the molar mass of gas component A and B, respectively. (m3/kmol) and (m3/kmol) are the molar volume of component A and B respectively, which are in liquid state and at normal boiling point.

Diffusion type is influenced by pore diameter d and molecular average free path λ, which can be determined by Knudsen number . can be expressed aswhere d is also the most probable pore diameter of material. The value of Kn and corresponding diffusion type are presented in Table 1. λ can be expressed as [22]where (Pa·s or kg/(m·s)) is the kinetic viscosity of gas, P (Pa) is the pressure, and M (kg/mol) is the molar mass. Relevant parameters of material IG-110 and BC, which are acquired by mercury intrusion porosimetry (MIP), are shown in Table 2.

Table 2: Pore parameters of carbon materials.
2.3. Seepage

Besides molecular diffusion, another possible transfer mechanism is convection, which can be defined as seepage in porous media. Seepage flow is a kind of viscous flow driven by pressure gradient. According to Darcy’s law, the seepage velocity u   (m/s) iswhere K (m2) is the permeability of porous material, which is influenced by porosity, pore diameter, tortuosity, etc. According to Timur formula [23], . In addition, research has shown that, for graphite, whose open porosity is about 10%, K is around 10−16 m2 [24].

2.4. Comparison of Transfer Mechanisms at Different Pressure

Different drying methods involve different pressure conditions. For the dehumidification of HTR-PM, the pressure of its working atmosphere Po (Pa) is 7 MPa, while for vacuum drying method and hot air drying method which are extensively adopted in experiment and industry, Po is vacuum and 0.1 MPa, respectively. The working pressure has a great influence on the moisture transfer mechanism in porous materials. A comparison is given in Table 3. In addition, the comparison is based on the following conditions: temperature is 250°C, the working atmosphere is helium, and the initial moisture content is 0.1%. Moisture content is defined aswhere (kg) is the dry material mass and (kg) is the moisture mass. In addition, both of the density of IG-100 and BC are set to 1700 kg/m3 in analysis.

Table 3: Comparison of transfer mechanisms at different pressure.

The comparison is discussed as follows. For hot air drying method, where Po = 0.1 MPa, the gas mixture in pores of material is binary, which consists of H2O and He. The released moisture can generate a high pressure Pi in pores, which can be 2.86 MPa in early stage as if all the absorbed moisture transforms to vapor. Then the pressure gradient between Pi and Po drives the seepage flow in pores. Meanwhile, molecular diffusion also exists. According to (5), molecular free path λ of H2O is about 114 nm (250°C, 0.1 MPa), while the most probable pore diameters d of IG-110 and BC are 2.5 μm and 30.3 μm, respectively, so Kn < 0.1, which means that the general diffusion dominates in pores. As for vacuum drying method, where Po < 0.1 MPa, only water vapor exists in pores and Knudsen diffusion also exists according to Kn. As for the dehumidification of HTR-PM, where Po = 7 MPa, seepage flow driven by the pressure gradient can be neglected and Pi can be considered constant; thus the gas diffusion coefficient D0 influenced by Pi is constant as well.

3. Mathematical Model

Two mathematical models for moisture transfer, diffusion model and diffusion-seepage model, are developed and presented here. In addition, the gas components in the equations below include H2O and He.

3.1. Diffusion Model

Diffusion model is based on molecular diffusion and Fick’s law. The governing equation for moisture mass in porous material iswhere (kg/m3) is moisture concentration.

3.2. Diffusion-Seepage Model

Diffusion-seepage model is based on diffusion and seepage, and the corresponding governing equation of moisture iswhere (kg/mol), (Pa·s or kg/(m·s)), and (kg/m3) are the molar mass, kinetic viscosity, and density of binary gas consists of H2O, and He, respectively.

The kinetic viscosity of binary gas is [25]where and are the volume percentages of H2O and He, respectively.

For the binary gas at 0.1 MPa, due to the relatively small proportion of He in pore, it has little effect on moisture transfer. Therefore, to simplify the governing Equation (9), can be considered as a constant and then the simplified equation is

4. Simulation and Result Analysis

4.1. Initial Parameters and Boundary Conditions

The dehumidification process of HTR-PM core has been simulated by using COMSOL Multiphysics software. Table 3 and (8) demonstrate the corresponding physical hypothesis and mathematical model, respectively.

The geometric model of HTR-PM core is shown in Figure 2. The internals in HTR-PM core mainly include the reflecting layer and insulation layer. Reflecting layer, mainly made of graphite bricks (IG-110), can be approximately considered as a cylinder, the dimension of which is 15600 mm in height and 4500 mm in outside diameter. In addition, the reflecting layer creates an interior space to contain fuel balls, the dimension of which is 11800 mm in equivalent height and 3000 mm in inside diameter. Insulation layer, mainly made of carbon bricks (BC), is also an approximate cylinder located outside the reflecting layer, the dimension of which is 4500 mm in inside diameter and 5000 mm in outside diameter. In addition, the thickness of top and bottom insulation layers is 400 mm and 800 mm, respectively. In fact, the horizontal cross section is not a perfect round but a regular polygon with 30 edges. Moreover, diameter of fuel ball is 60 mm. During the dehumidification process, the helium flow (250°C, 7 MPa) takes the moisture away from internals. Helium flows up from core bottom to cold gas chamber through cold gas channel and then flows down to hot gas chamber through core chamber and leaves the core at last.

Figure 2: Internals in HTR-PM core.

Some simplifications of geometric model are adopted here. The neutron source channels, absorption ball channels, hot gas duct, dowels and keys, gap between graphite and carbon bricks, and so on are neglected. Thus, the internals model can be divided into 30 same trigonal prism modules, one of which is shown in Figure 2(b). Each module is mirror symmetrical to the adjacent one. Therefore, we can adopt only one module to represent the moisture transfer process in the whole core internals. In addition, pore structure of materials features isotropy, and the material parameters of fuel ball are considered the same as graphite IG-110.

The mass transfer process is considered as internal diffusion controlled, so the first kind of boundary condition is adopted to the model, which means moisture content on the boundary, surface of which is exposed to helium atmosphere, is constant. Then is adopted in this simulation. In addition, the kinetic viscosity of gas is considered constant due to the very small effect of pressure variation.

Some key parameters adopted in simulation are presented in Table 4.

Table 4: Some parameters of model (250°C, 7 MPa).
4.2. Result Analysis of Simulation

According to the numerical simulation, the distribution of moisture content (%) in HTR-PM core at time t = 50 d is shown in Figure 3, where d represents units day. It can be found from Figure 3(a) that moisture mainly concentrates at the top, bottom, and side of core. Figure 3(b) presents the moisture distribution at the axial cross section. It can be found that the maximum locates at the top of core. In addition, Figure 3(c) and Figure 3(d) further demonstrate the moisture distribution at the top and bottom surface, respectively. It can be seen that near the cold gas and control rod channels, fuel feed tube, and fuel discharge tube is relatively low, while it is much higher elsewhere.

Figure 3: Distribution of (%) in HTR-PM core (t = 50 d).

The curves of moisture content versus time are shown in Figure 4. It can be found that the average moisture content of internals and fuel ball decreases exponentially, in which it can be explained that moisture content decreases much faster in the early stage because of the high moisture concentration gradient and decreases slower in the later stage as a result of the decrease of concentration gradient. of fuel ball decreases far faster than that of core internals. Thus, the internals, not fuel balls, are the major limiting factor for the dehumidification. It can also be found that the required time to reach = 0.02%, 0.01%, and 0.005% of whole internals is 43 d, 72 d, and 108 d, respectively. In addition, of reflecting layer (IG-110) decreases much faster than that of insulation layer (BC), which can be attributed to the larger open porosity of IG-110. Thus effective diffusion coefficient of IG-110 is much larger, which promotes the moisture transfer.

Figure 4: Curves of moisture versus time.
4.3. Sensitivity Analysis

In order to accelerate the moisture transfer to improve the dehumidification efficiency, it is reasonable to promote the molecular diffusion and seepage flow. According to the relations, and , molecular diffusion can be promoted by increasing the temperature T and decreasing the system pressure Po, while seepage can be promoted by increasing the pressure gradient, which can be achieved by decreasing the system pressure .

The influence of temperature T on dehumidification of HTR-PM is shown in Figure 5(a), where Cr,a on Y-axis denotes the average moisture content of whole internals obtained by simulation. It can be found that the dehumidification efficiency increases as temperature increases. Figure 5(b) presents the influence of system pressure on dehumidification, and it shows that the dehumidification efficiency of 0.1 MPa is certainly much higher than that of 7 MPa. In addition, in the simulation where MPa, the diffusion-seepage model is adopted and is considered constant to simplify the computation.

Figure 5: Curves of moisture versus time at different temperature and pressure.

As for the actual dehumidification for HTR-PM, T = 250°C and Po = 7 MPa. Since the temperature is already pretty high, the promotion by increasing temperature is limited, while as for the system pressure, if it is reduced greatly from 7 MPa to 0.1 MPa, this change will promote both the diffusion and seepage significantly. But on the other hand, the decrease of pressure is not advantageous for the core to be heated. It is because the heat of core is transformed from mechanical energy of helium circulator; thus the heating power is relatively low at low pressure.

4.4. Analytical Solution

In order to obtain an analytical solution of the mathematical model, the irregular geometric model of core internals can be represented by an infinite plate, whose characteristic length (m) is the same as that of irregular geometry. In addition, , where V (m3) and (m2) are the volume and effective surface area of geometry, respectively.

The infinite plate with thickness is shown in Figure 6. Diffusion model (8) is adopted. The moisture content is , and effective diffusion coefficient is constant. Thus, the governing equation can be rewritten asThe boundary condition is . The initial condition is . Thus, the analytical solution, which is an infinite series, can be obtained aswhere (, and is an integer), , and .

Figure 6: Infinite plate.

In order to simplify the solution, only the first polynomial of (13), which means , is adopted. Thus, the average moisture content can be calculated, which isAs for the geometric model of internals of HTR-PM, according to the statistic obtained in Solidworks software, its is 0.3066 m. In addition, considering and %, the analytical solution for dehumidification of HTR-PM can be obtained.

Figure 7 shows the comparison between analytical and numerical simulation. It is found that curves Cr,a-t of analytical and numerical solution of infinite plate are in good agreement. While comparing curves of analytical and numerical solution of HTR-PM, it is found that the agreement is not that good. It is suggested that the simplified analytical solution is pretty accurate for an ideal regular geometry model, while it is difficult to obtain the characteristic length Lc to accurately represent an irregular geometry. The uneven distribution of channels, chambers, and other irregular structures in reactor core results in the deviation of solution. It is also suggested that, in order to derive a more representative Lc, some optimization methods can be adopted to the calculation of Lc, e.g., introducing empirical correction coefficient, dividing the whole geometry into several sections, etc.

Figure 7: Comparison of analytical and numerical solutions.

5. Conclusion

In the dehumidification process of HTGR, the major moisture transfer mechanism in carbon materials includes molecular diffusion and seepage. Thus, diffusion model and diffusion-seepage model are developed to describe the dehumidification process of internals in reactor core. The simulation result of dehumidification of HTR-PM suggests that the average moisture content of internals decreases exponentially with time and the moisture mainly concentrates in the top and bottom of core. According to the sensitivity analysis, the dehumidification efficiency can be promoted by the increase of temperature and decrease of system pressure, especially by reducing the system pressure, and the dehumidification efficiency can be greatly improved. The analysis on analytical solution of dehumidification problem shows that the simplified analytical solution is pretty accurate for an ideal regular geometry model, while the calculation of characteristic length of irregular geometry needs to be improved.

Data Availability

The data used to support the findings of this study are included within the article.

Conflicts of Interest

The authors declare that they have no conflicts of interest.

Acknowledgments

This work was supported by the National Natural Science Foundation of China (NSFC) (Grant no. 11302117), Beijing Natural Science Foundation (Grant no. 2182023), and the Chinese National S&T Major Project (Grant no. ZX06901).

References

  1. D. V. Ragone, W. V. Goeddel, and L. R. Zumwalt, “Graphite-matrix nuclear fuel systems for the peach bottom HTGR,” J. Annealing, 1963. View at Google Scholar
  2. S. J. Xu and F. Y. Kang, Carbon and Graphite Materials in Nuclear Engineering, M. Tsinghua University Press, 2010.
  3. T. L. Albers, “High-Temperature Properties of Nuclear Graphite,” Journal of Engineering for Gas Turbines and Power, vol. 131, no. 6, Article ID 064501, 2009. View at Google Scholar
  4. Z. Zhang, Z. Wu, Y. Sun, and F. Li, “Design aspects of the Chinese modular high-temperature gas-cooled reactor HTR-PM,” Nuclear Engineering and Design, vol. 236, no. 5-6, pp. 485–490, 2006. View at Publisher · View at Google Scholar · View at Scopus
  5. L. S. Wang, Y. C. Fang, F. Wu et al., “The position of boron carbide in nutron absorbing materials and its properties relation to nuclear application,” J. Materials Science and Engineering of Powder Metallurgy, vol. 2, pp. 113–120, 2000. View at Google Scholar
  6. Z. Zhang, J. Liu, S. He, Z. Zhang, and S. Yu, “Structural design of ceramic internals of HTR-10,” Nuclear Engineering and Design, vol. 218, no. 1-3, pp. 123–136, 2002. View at Publisher · View at Google Scholar · View at Scopus
  7. X. Zhou, Y. Tang, Z. Lu, J. Zhang, and B. Liu, “Nuclear graphite for high temperature gas-cooled reactors,” New Carbon Materials, vol. 32, no. 3, pp. 193–204, 2017. View at Publisher · View at Google Scholar
  8. L. U. Zhen-ming, X. T. Chen, and L. Q. Wei, “Pore structure and moisture absorption property of carbon materials in HTR,” Journal of Atomic Energy Science and Technology, vol. 50, no. 3, pp. 477–483, 2016. View at Publisher · View at Google Scholar
  9. J. R. Morris, C. I. Contescu, M. F. Chisholm et al., “Modern approaches to studying gas adsorption in nanoporous carbons,” Journal of Materials Chemistry A, vol. 1, no. 33, pp. 9341–9350, 2013. View at Google Scholar
  10. M. Steinbrück, “Oxidation of boron carbide at high temperatures,” Journal of Nuclear Materials, vol. 336, no. 2-3, pp. 185–193, 2005. View at Publisher · View at Google Scholar
  11. P. Wang, Y. Wang, and S. Y. YU, “Characterization of porosity development in oxidized nuclear graphite,” J. Science & Technology Review, vol. 30, no. 20, pp. 21–26, 2012. View at Google Scholar
  12. R. P. Wichner, T. D. Burchell, and C. I. Contescu, “Penetration depth and transient oxidation of graphite by oxygen and water vapor,” Journal of Nuclear Materials, vol. 393, no. 3, pp. 518–521, 2009. View at Publisher · View at Google Scholar · View at Scopus
  13. C. I. Contescu, T. Guldan, P. Wang, and T. D. Burchell, “The effect of microstructure on air oxidation resistance of nuclear graphite,” Carbon, vol. 50, no. 9, pp. 3354–3366, 2012. View at Publisher · View at Google Scholar · View at Scopus
  14. X. L. Yu, X. Y. Yang, and S. Y. YU, “Present status of research on the oxidation of graphite in case of air and water leakage in HTR,” Journal of Nuclear Power Engineering, pp. 313–315, 2006. View at Google Scholar
  15. P. Wang, C. I. Contescu, S. Yu, and T. D. Burchell, “Pore structure development in oxidized IG-110 nuclear graphite,” Journal of Nuclear Materials, vol. 430, no. 1-3, pp. 229–238, 2012. View at Publisher · View at Google Scholar · View at Scopus
  16. X.-L. Yu, X.-W. Luo, and S.-Y. Yu, “Simulation of oxidation in HTR-10 core,” Hedongli Gongcheng/Nuclear Power Engineering, vol. 31, no. 2, pp. 81–97, 2010. View at Google Scholar · View at Scopus
  17. J. Y. Dou and H. Q. Yin, “Preliminary investigation into the dehumidification model of HTR-PM initial core,” in Proceedings of the 14th National Symposium on Reactor Thermal Fluid, Beijing, China, 2015.
  18. X. D. Liu and B. B. Yang, “Review and vista on drying theories of porous medium,” Journal of China Agricultural University, vol. 10, no. 4, pp. 81–92, 2005. View at Google Scholar
  19. W. Xu, L. SHI, Y. H. Zheng et al., “Research on oxidation model of nuclear grade graphite IG-110,” Journal of Atomic Energy Science and Technology, vol. 49, pp. 475–480, 2015. View at Google Scholar
  20. P. Wang and S. Y. Yu, “Study on model of nuclear graphite oxidation,” Journal of Atomic Energy Science and Technology, vol. 46, no. 1, pp. 84–88, 2012. View at Google Scholar
  21. Z. Chen, P. Zhou, and C. Mei, “Principle of transportation processes,” M. Central, pp. 333–337, 2011. View at Google Scholar
  22. Z. S. Ji, R. K. Zhu, and D. Li, Principle of transmission, M. Harbin Institute of Technology Press, Harbin, China, 2002.
  23. F. H. Clarke, R. J. Stern, and P. R. Wolenski, “Proximal smoothness and the lower C2 property,” Journal of Convex Analysis, vol. 2, no. 1, pp. 117–144, 1995. View at Google Scholar
  24. Q. Liu and Y. F. Hu, Study on Non-linear Seepage Flow Law in Carbon Graphite and Impregnated Antimony Experimental Analysis, D. China Mining University, Xuzhoum, China, 2010.
  25. L. Kong, Engineering Fluid Mechanics, vol. 7, M. China Electric Power Press, Beijing, China, 2010.