3.1. Modeling for APR1400 Benchmark Problems
The Korea Atomic Energy Research Institute has released an APR1400 benchmark problem book [
21]. This benchmark problem loads the 241 CE (combustion engineering)-type 16 × 16 fuel assemblies and has a total thermal power output of 3983 MW. These assemblies are categorized into A, B, and C types, with the B and C types further divided into four variants (indexed 0–3) based on radial enrichment zoning patterns and the number of Gadolinia burnable absorber pins.
Figure 5 shows the loading pattern and the locations of control rods, including two shutdown banks (A and B) and five regulating banks (R1 to R5). The shutdown banks and some regulating banks are equipped with 12-finger type control rods, while others have 4-finger type control rods.
The benchmark sets consist of six categories: (1) single fuel pin problems (APR01), (2) 2D fuel assembly problems (APR02), (3) 2D core problems (APR03), (4) 3D core problems (APR04), (5) control rod worth problems (APR05), and (6) 3D core depletion problem (APR06).
Table 1 summarizes the nine conditions of the APR02 to APR04 benchmark problems, while
Table 2 details the control rod conditions for APR05. Unfortunately, the benchmark book does not include depletion results for APR06.
In this study, we focused on evaluating the computational efficiency and accuracy of the proposed modified 2D/1D decoupling method (2D1DBOX) through analysis of the 3D core problem (APR04) and the control rod worth problem (APR05). Four-group pin-wise homogenized group constants (GCs) were generated via conventional 2D lattice calculations performed by KARMA, supplemented by corresponding SPH iterations. For the reflector regions, pin-wise homogenized GCs were determined following the methodology outlined in previous work [
17].
While the APR1400 benchmark book provides reference solutions obtained using McCARD [
21], it lacks pin-wise information. Therefore, in this study, solutions derived from 3D calculations using KARMA were considered as the reference solutions. The model adhered to the specifications provided in the benchmark, with each pin-cell modeled to include all components, such as the pellet, air gap, cladding, and moderator. The fuel pellet was subdivided into 40 flat source regions (FSRs) by 5 annular rings and 8 azimuthal sections, and the number of annular rings was increased to 8 for the burnable poison pellet. Similarly, the moderator region was subdivided into 32 FSRs by 4 annular rings and 8 azimuthal sections. This FSR subdivision ensured accurate consideration of sub-pin level flux variations.
Each fuel assembly comprised 3 bottom reflector planes, 30 active fuel planes, and 3 top reflector planes. The active fuel planes were loaded with detailed models for fuel, burnable poison, and guide and instrument tube pin-cells. Additionally, the water gap was explicitly modeled, while the nine spacer grids were semi-explicitly modeled by smearing ZIRLO in the moderator. In the axial reflector planes, the fuel bottom and top ends and the guide and instrument tubes were explicitly modeled, while other structures, such as the core plate, bottom and top nozzles, etc., were smeared in the moderator.
The core loaded with 241 fuel assemblies was surrounded by an assembly-thick water reflector with an explicitly modeled stainless steel shroud. However, other structures, such as the core vessel and neutron pads, were not included in the model.
For a fully consistent code-to-code comparison, the KARMA2 core model was used to generate pin-homogenized four-group cross sections (XSs). Notably, the lower energy boundaries of the four-group were established at 9.119 × 10
3, 3.928, 6.251 × 10
−1, and 1.000 × 10
−4 eV, determined as optimal in previous studies [
12,
17]. KARMA2 calculations were performed using a 47-group (47G) transport-corrected P0 (TCP0) XS library based on ENDF/B-VII.1. The ray parameter set featured 0.02 cm ray spacing with 16 azimuthal and 3 polar angles per octant sphere and was used for the 3D core calculations.
The pin-wise XSs and 4G fluxes for fuel assemblies were obtained from 2D single assemblies with all reflective boundary conditions. Meanwhile, the XSs and fluxes for radial and axial reflectors were derived from fuel-reflector local problems. Pin-wise SPH factors were determined using the standard procedure, using the corresponding coarse group XSs and fluxes.
3.2. Computing Performance of 2D/1D Decoupling Methods
Table 3 outlines the required calculation time for each module of the method. For the test problem, an un-rodded APR1400 core (APR04V05) was selected. Notably, the 2D1DBOX method significantly reduced computation time, particularly in the 1D FDM module, which constituted the largest segment (approximately 64%) of the 2D1D method. Despite the additional iterations required in the 2D FDM and 3D CMFD modules, the increase in computation time was negligible compared to the significant time reduction achieved in the 1D FDM module.
To evaluate the parallel performance of both methods, the APR04V05 problem was solved using various numbers of threads. The calculations were parallelized using the OpenMP platform and executed on a Linux system featuring an Intel
® Xeon
® Platinum 9242 processor (Intel, Santa Clara, CA, USA).
Figure 6 shows the total execution time and speed-up factor against the number of threads. Speedup is defined as ratio of single-thread calculation time to multi-thread calculation time to represent the performance of multi-threading. With a single thread, the total execution time of the 2D1D method was approximately 86.2 s, reduced to 6.6 s with 32 threads. It is worth noting that the execution time of the current 2D1D-based pin-by-pin core calculation was significantly shorter than in previous studies [
17]. Furthermore, the execution time was further reduced with the proposed 2D1DBOX method, requiring approximately 39.8 s and 3.6 s with a single thread and 32 threads, respectively. With 32 threads, the 2D1DBOX method saved approximately 45% of computing time. However, the speed-up factor of the 2D1DBOX method was lower than that of the 2D1D method owing to the smaller number of 1D FDM problems.
As mentioned in the previous section, the proposed 2D1DBOX method was based on the observation of box (or node)-wise similarity in axial leakage. Therefore, it was imperative to validate the accuracy of the 2D1DBOX method when applied to axially heterogeneous problems, such as rodded cases.
Table 4 and
Table 5 present the discrepancies in the major design parameters between the two methods for the rodded problem of APR05V05. Fr and Fq are an axially integrated radial peaking factor and a 3D peaking factor, respectively. Fxy is maximum value of planar radial peaking factor, Fxy(z). It is worth noting that the difference between the two methods was negligible in terms of nuclear design accuracy.
3.3. Accuracy of Pin-by-Pin Core Calculation
Table 6 presents the pin-wise calculation results of the APR04 benchmark problems compared to the reference solution obtained with KARMA.
Figure 7,
Figure 8,
Figure 9,
Figure 10,
Figure 11,
Figure 12,
Figure 13,
Figure 14 and
Figure 15 show each variant’s reference normalized 2D pin-power distribution and the relative pin-power error distribution. The normalized 2D pin-power distribution was axially integrated pin-power distribution and normalized by a factor which made the average ‘one’. The eigenvalue differences across all variants were below 50 pcm, and the error in fuel assembly (FA) power was smaller than the typical value obtained through conventional nodal analysis. Regarding the relative pin-power error, maximum values were below 4%, and the root mean square (RMS) values were below 1%, except for the cold zero power (CZP) conditions (V01, V04, V07). The maximum values of all variants were located at pins which had relatively small pin power, around 0.2~0.3. Therefore, the actual effect of maximum pin power error was not much.
Table 7 shows additional analyses of the pin-power distribution. First, the pin-power error of the radial peak pin was acceptably small. Second, the maximum pin-power error was evaluated again using only pin-power values greater than average value (1.0). This was to obtain more meaningful pin-power error information by excluding practically meaningless data. Hereinafter, this pin-power error will be referred to simply as “effective max. pin-power error”. As expected, the effective max. pin-power errors were below 2%, except for the CZP conditions.
Based on the results presented in
Table 6 and
Table 7, discrepancies in the CZP conditions slightly surpassed those in hot zero power (HZP) and HFP conditions. This discrepancy can be attributed to the “outward” power distribution observed in the CZP conditions, as shown in
Figure 7,
Figure 10 and
Figure 13.
Similar to conventional two-step procedures, the pin-wise core analysis in this study also exhibited an inherent limitation, leading to discrepancies when the pin-wise GCs were not applied in areas where they were originally generated. Disagreements arose in fuel assemblies that faced the baffle-reflector or a different type of FA because the pin-wise GCs were generated in a FA problem with all-reflective boundary conditions. Additionally, in the CZP condition, the peripheral fuel assemblies had relatively high power (“outward” power distribution) and steeper gradients in the pin-power distribution compared to other conditions, as illustrated in
Figure 16. Despite resulting in relatively high effective max. pin-power errors (4–6%) in the peripheral fuel regions, they were not important owing to significantly small pin powers in the cold “zero power” condition.
Figure 17 shows the axial power distribution and relative axial power error distribution. This axial power distribution was determined by radially integrating power distribution of each layer. The pin-by-pin solution demonstrated good agreement with the reference KARMA solution, with most axial power errors below 0.8%.
Table 8 presents the pin-wise calculation results of the rodded benchmark problems. The eigenvalue differences across all variants were below 31 pcm. Compared to conventional nodal analysis, the pin-by-pin calculation showed better agreement in FA power error, with errors smaller than typical values obtained through conventional nodal analysis. The maximum and RMS values of the relative pin-power error were below 4% and 1.3%, respectively. Upon inserting all control rods, including the two shutdown banks, the pin-power errors marginally increased compared to the un-rodded problem (APR04V02). The maximum value shifted from −2.43% to −3.98%, and the RMS value changed from 0.84% to 1.05%. The maximum value of V07, −3.98%, was located at a fuel pin just next to the R3 control bank. It is noted that the corresponding fuel pin was in the B0 type FA, which was loaded in a peripheral region of the APR1400 core, and the normalized pin-power of corresponding fuel pin was around 0.36.
Table 9 shows that the pin-power errors of the radial peak pin ranged from 1% to 2% or below. The effective max. pin-power errors were around 3% or below. This accuracy is much better than that of the conventional nodal code.
Table 10 presents the control rod worth for both cumulative and group-wise banks. The cumulative control rod worth represents the total control rod worth of the rodded banks. In contrast, the group-wise control rod worth is the individual group control rod worth under the control rod insertion sequence detailed in
Table 2. For the pin-by-pin calculations, the error range of the cumulative and group control rod worth was between −0.59% and 0.62% and between −1.16% and 1.51%, respectively.
Figure 18 illustrates the axial power distribution and axial power error distribution of a representative rodded benchmark problem. Similar to the un-rodded case, the pin-by-pin solution demonstrated excellent agreement, with errors below 1.0%.