# Modeling of SPERT IV Reactivity Initiated Transient Tests in EUREKA-2/RR Code

Authors: N. H. Badrun; M. H. Altaf; M. A. Motalab; M. S. Mahmood; M. J. H. Khan
Journal: International Journal of Nuclear Energy
 (2014)

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## Abstract

EUREKA-2/RR code has been used for SPERT IV reactor benchmark calculations against the experimental results provided by IAEA (International Atomic Energy Agency) obtained for a series of transient tests initiated by step insertion of different magnitudes of positive reactivity with varying degrees of different controlled parameters such as reactor initial power, coolant temperature and coolant flow condition. 20 out of 39 tests that fall under forced convection mode have been considered for the present simulation provided the reactor scram system is disabled. Peak power and peak clad temperature due to transient have been calculated and it was found that although peak clad temperature values agreed, the peak power values seem to underestimate the experimental values. Further study appears to be needed to identify the limitations in modeling or examining the effect of input parameters during modeling to obtain the better simulation results.


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## Body

## 1. Introduction

Since SPERT program initiated in 1954, a variety of configurations under a broad range of conditions have been taken into consideration to study transient behavior of nuclear reactors. With the growing need to validate the experimental results, numerical code has got much attention and PARET is one such computer code originally developed for the analysis of SPERT-III experiments in 1969 [1]. Later, this code has been modified incorporating many issues such as selection of flow instability, departure from nucleate boiling, single- and two-phase heat transfer correlations, and a properties library considered more applicable to the low pressures, temperature, and flow rates that enhances the acceptability of the code for its subsequent use in the analysis of transient behavior of research reactor. However, in modeling the research reactor transient condition, the analyst has to consider some conservative assumptions due to lack of experimental data which may lead to false prediction of the real physical phenomenon that takes place in the reactor. One common point that came out from reactor analysis is the importance of proper selection of input parameters such as DNB correlations to obtain the real characteristic of the transient parameters [2, 3]. In this context, reactivity initiated transient analysis code EUREKA-2/RR [4] has been used whether it could be able to model the SPERT IV transient experiment. This work has been done under the framework of the International Atomic Energy Agency Coordinated Research Project (CRP) 1496 “Innovative Methods in Research Reactor Analysis: Benchmark Against Experimental Data on Nuetronics[sic] and Thermal Hydraulic Computational Methods and Tools for Operation and Safety Analysis of Research Reactors,” the aim of which is to develop the innovative research reactor modeling methods and to assess and qualify the computational codes for application in the safety analysis of various research reactors. Being the member of this CRP project, the authors have been delivered the design specifications with tests results of SPERT IV transient experiment for analysis with the computer code they have.


## 2. SPERT IV Transient Tests Description

The SPERT IV D-12/25 core was a light water-cooled and moderated, pool-type reactor with provisions for both upward forced and natural convection cooling. The core is composed of 25 type-D standard fuel assemblies in a square five by five section of the nine by nine supporting grid. The core configuration is provided in Figure1. Each standard fuel assembly contained 12 removable fuel plates. Four gang-operated boron-alloy double-blade control rods and one transient rod of the same style located in the center of the core were accommodated in the standard fuel assembly replacing its six fuel plates. For complete specification of the reactor components, Day [5] can be referred to. The test sequence is illustrated in Figure 2 where five transient phases are noticed. There are 39 transient tests reported for SPERT IV reactor benchmark analysis [5]. The published results for peak power, peak cladding temperature, and energy released are provided in the document [5] with respect to a number of control variables such as initial reactor power, reactivity insertion, bulk moderator-coolant temperature, hydrostatic head, and coolant circulation rate. Table 1 shows these tests are divided into five groups in terms of coolant flow rate. The first group corresponds to flow rate zero with coolant velocity zero, the second group corresponds to 500 gpm with coolant velocity 0.365 m/s, the third group corresponds to 1000 gpm with coolant velocity 0.731 m/s, the fourth group corresponds to 2500 gpm with coolant velocity 1.828 m/s, and the fifth group corresponds to 5000 gpm with coolant velocity 3.657 m/s. Also, each test of each group is seen to differ with respect to initial ambient reactor temperature, power, reactivity insertion, and corresponding period. It is also apparent that the tests in each group were performed in a progressive manner by increasing the amount of positive insertion of reactivity so the corresponding transient period is found shorter. Most of the tests in the series were initiated with the reactor critical at a power level of approximately 1 W which is related to the initial transient period >15 ms. The remaining tests were performed for <15 ms for which the reactor was initially subcritical at a power in the milliwatt range that allows the complete reactivity insertion before power rises to a significant level.Table 1
Transient tests for SPERT IV.
Group
Test number
Reactivity ($)
Period (msec)
T
i (°C)
Flow (gpm)
Initial power (W)
1
B1
0.80
980
19.0
0
1
B2
0.88
598
20.0
0
1
B3
0.92
374
21.8
0
1
B4
0.98
190
20.9
0
1
B5
1.04
107
22.2
0
1
B6
1.11
62.4
22.4
0
1
B7
1.15
49.8
22.2
0
1
B8
1.26
29.6
22.4
0
1
B9
1.40
19.6
22.4
0
1
B10
1.53
15.8
20.5
0
1
B11
1.54
14.5
22.2
0
0.001
B12
1.68
11.7
22.3
0
0.001
B13
1.82
10.1
22.2
0
0.001
B14
1.91
8.48
22.0
0
0.001
B15
2.00
7.83
19.9
0
0.001
B16
2.14
7.0
19.8
0
0.001
B17
1.40
21.3
22
0
1
B18
1.68
12.0
21.8
0
0.001
B19
1.91
8.83
21.7
0
0.001
2
B20
0.88
560
21.9
500
1
B21
1.14
54.2
22.8
500
1
B22
1.66
11.9
23.3
500
0.001
B23
1.80
10.1
23.2
500
0.001
3
B24
0.88
529
22
1000
1
B25
1.04
103
22.5
1000
1
B26
1.14
54.5
22.8
1000
1
B27
1.39
20.0
23
1000
1
B28
1.66
12.3
22.9
1000
0.001
B29
1.80
10.4
22.9
1000
0.001
4
B30
0.88
531
22.5
2500
1
B31
1.14
52.1
22.7
2500
1
B32
1.66
12.2
22.6
2500
0.001
B33
1.80
10.0
23.2
2500
0.001
5
B34
0.88
516
21.9
5000
1
B35
1.05
104
22.0
5000
1
B36
1.14
49.3
22.4
5000
1
B37
1.39
20.7
20.7
5000
1
B38
1.66
12.2
23.4
5000
0.001
B39
1.80
10.1
23.7
5000
0.001Figure 1
SPERT1V D-12/25 core configuration.Figure 2
Sequences followed in reactivity insertion tests of SPERT IV D-12/25 core.It is to mention that the initial power columned in Table1 is not directly provided in the SPERT IV documentation. This initial power was considered as 1 W for transient period >15 ms and was considered at milliwatt range for transient period <15 ms. Only tests with forced upward coolant flows 500 gpm, 1000 gpm, 2500 gpm, and 5000 gpm were taken into consideration for the present simulation. These ranges of tests are found to consider 18 ft hydrostatic head.


## 3. EUREKA-2/RR Code and Modeling the SPERT IV Core

EUREKA-2/RR is a revised version of EUREKA-2 which was originally developed by JAEA for reactivity accident analysis for nuclear power plants. A heat transfer package is added to EUREKA-2 to modify it to EUREKA-2/RR where the heat transfer correlations considered in the heat transfer package were obtained or estimated from the heat transfer experiments in which the thermal hydraulic features of the upgraded JRR-3 core were properly reflected. This causes the EUREKA-2/RR to be more applicable to research reactors which are operated under low pressure and low temperature conditions using plate-type fuel, just like the JRR-3M. In this special heat transfer package, for heat transfer coefficients of single-phase flow, Dittus-Boelter correlation is used for forced convection mode and Collier correlation for natural convection mode; Chen correlation is used for heat transfer coefficients of two-phase flow and then ONB (onset of nucleate boiling) is determined by comparing the heat flux predictions from Dittus-Boelter correlation and the modified Chen correlation. When the heat flux by the modified Chen correlation is greater than the heat flux by the Dittus-Boelter correlation, it is justified that the nucleate boiling starts under the saturation condition or under the subcooled condition [5]. For DNB heat flux calculation, the code used Sudo-Kaminaga correlation based on JRR-3 thermal hydraulic experiment [6]. One-dimensional time dependent heat conduction equations are used for heart conduction model. The thermal hydraulic solution is assumed to contain one-dimensional homogeneous fluid with the vapor and liquid phases in thermodynamic equilibrium.EUREKA-2/RR does RIA analysis by coupling neutronics, thermal hydraulics, and point kinetics, as shown in Figure3. Hence, calculation of neutronics is of first consideration and MVP code [7] has been used for this purpose. Kaminaga developed three supporting codes which are DISSUE, ICETEA, and PREDISCO [8] to produce necessary input for developing model in EUREKA-2/RR. DISSUE calculates power fraction and reactivity weighting factors for each heat slab, ICETEA produces coolant temperature distribution, and PREDISCO calculates coolant pressure distributions for different volumes of corresponding channels.Figure 3
An outline of the process followed in preparing input of EUREKA-2/RR.For modeling SPERT IV core in EUREKA-2/RR code, only fuel region with upper and lower plenum was considered. The whole core was divided into several regions called channels in the code. These channels differ from each other by power generation, coolant mass flow rate, and hydraulic diameters. The core contains 20 standard fuel assemblies and 5 control fuel assemblies. Each standard fuel assembly contains 12 fuel plates and each control fuel assembly contains 6 fuel plates. All these fuel assemblies are distributed into 5 distinct channels. The distribution of these fuel assemblies among the channels is made on the basis of what value of radial power peaking factors,F
R, each fuel assembly contains. Table 2 provides the average radial peaking factors calculated for each fuel assembly. The computer code MVP version 2.0 [5] has been used for neutronics calculation considering cold, clean SPERT IV core using the cross-section library based on JENDL-3.3 [9]. Initially, the fuel assemblies have to be arranged in decreasing order of F
R that starts from the maximum value of 1.37322 as seen in Table 2. Channel-1 is chosen as the hottest channel that contains a single fuel plate of the hottest fuel assembly E6 with the maximum F
R. Accordingly, channel-2 contains the remaining fuel plates of E6 along with the other 7 fuel assemblies, channel-3 contains 10 fuel assemblies, channel-4 contains 2 fuel assemblies together with 2 control fuel assemblies, and channel-5 contains the last three control fuel assemblies. Also, the axial peaking factor distribution calculated for the hottest fuel plate is given in Figure 4. The fuel assemblies in each channel are defined by heat conductors called heat slabs while the coolant in the channel is represented by several nodes and junctions. In the present model, each channel consists of 10 heat slabs along with 10 nodes (volumes) and 11 junctions as shown in Figure 5. The model in total then consists of 52 volumes, 50 heat slabs, and 56 junctions. According to Figure 5, junction number 56 is the fill junction used to simulate the primary coolant flow in the core. Coolant mass flow rates along the channels for different flow rates are provided in Table 3. Table 4 contains the kinetic parameters that were used during simulation [5]. Other necessary input parameters are taken also from the report of Day (2009) [5]. However, some parameters such as friction and resistance coefficients, fuel and cladding thermal properties, and plenum characteristics have been approximated due to unavailability of the data.Table 2
Channel distributions in EUREKA-2/RR.
Fuel cell number
Radial peaking factors (MVP)
Channels
Number of fuel cells
Number of fuel plates
E6
1.37322
1
1/12
1
E6
1.37322
2
7 + 11/12
95
F5
1.37105
E4
1.36998
D5
1.36887
E7
1.15432
G5
1.14816
E3
1.14151
C5
1.13272
D7
1.04837
3
10
120
F7
1.04519
D3
1.04256
G6
1.04235
F3
1.04180
G4
1.04120
C6
1.03932
C4
1.03897
C7
0.83797
G3
0.83581
C3
0.83525
4
4
36
G7
0.83392
E5
0.81652
F6
0.61168
D6
0.61119
5
3
18
F4
0.60960
D4
0.60847Table 3
Coolant mass flow rate distributions along the channel.
Core flow rate
Channel-1
Channel-2
Channel-3
Channel-4
Channel-5
gpm
Kg/sec
500
0.1520
14.4500
18.2535
6.0849
3.6515
1000
0.3041
28.9000
36.5093
12.1706
7.3035
2500
0.7600
72.2500
91.2675
30.4245
18.2575
5000
1.5205
144.5040
182.5465
60.853
36.5175Table 4
Kinetic parameters used for SPERT IV transient analysis.
Parameters
Values
Moderator temperature feedback coefficient (20–35°C)
−1.2¢
Void feedback coefficient
−41.5¢/% decrease in moderator density
Prompt neutron lifetime
6.4 × 10−5 sec
Effective delayed neutron fraction (—)
0.0069Figure 4
Axial peaking factors along the hottest plate.Figure 5
Schematic diagram of the model prepared for EUREKA-2/RR analysis.


## 4. Results and Discussion

The calculated peak power values together with the experimental values for observed tests under forced convection are summarized in Table5. It is seen that the calculation has provided peak power values which are too low compared to the experimental values and these underestimating the experimental measure in most cases exceed by an amount from 60% to 70%. But for peak clad temperature estimation, this difference is found in comparison to be largely reduced. Figures 6 to 9 present comparison between experimental and calculation results of peak clad temperature for all the tests identified as B20 to B39.Table 5
Peak power (MW) results for tests with forced flow.
Test number
Flow rate
Measurement
EUREKA-2/RR
B20
500 gpm
—
0.9
B21
21.5
7.1
B22
322.0
77.5
B23
435.0
150.7
B24
1000 gpm
—
0.9
B25
7.5
1.7
B26
22.5
6.3
B27
130.0
37.2
B28
292.0
101.7
B29
425.0
150.7
B30
2500 gpm
—
0.9
B31
22.5
6.3
B32
320.0
99.4
B33
435.0
153.1
B34
5000 gpm
—
0.9
B35
9.8
2.4
B36
30.2
6.4
B37
169.0
37.5
B38
370.0
102.3
B39
505.0
148.5Figure 6
Peak clad temperature values for the tests of group 2.Figure6 is for group 2 with 500 gpm flow rate which consists of four tests identified as B20, B21, B22, and B23. Figure 8 presents group 4 that contains four tests B30, B31, B32, and B33 but with different flow rate, 2500 gpm. Similarly, Figure 7 presents group 3 with 6 tests with the identifications B24, B25, B26, B27, B28, and B29 with coolant flow rate 1000 gpm and Figure 9 reflects group 5 with six tests B34, B35, B36, B37, B38, and B39 with flow rate 5000 gpm. It is evident from these plots that results of EUREKA-2/RR code and SPERT IV tests vary within 12% for almost all the tests. However, some inconsistency is noticed for few tests which correspond to a reactivity insertion less than $1. If one traces back work of Chatzidakis et al., 2012 [3], it is found that three DNB correlations, namely, Tong, Mirshak, and Bernath, facilitated in the PARET code, have been applied for a range of tests to identify use of which correlation provides peak clad temperature values that agree with the experimental results. Peak power values have not been shown to compare with the experiment in this paper. It is identified in this paper that the peak clad temperature values estimated using the Tong DNB correlations provide results that vary within 50% with experimental results wherever it seems that Mirshak and Bernath correlation fail to incorrectly predict the system response. In contrast EUREKA-2/RR code does not contain Tong, Mirshak, and Bernath correlations but it has Sudo-Kaminaga correlation for DNB heat flux calculations. Although peak clad temperature values are found to agree reasonably well with the experiment, the difference between code and experiment in calculation of peak clad temperature with the experiment whether due to the DNB correlation or other parameters needs to be identified.Figure 7
Peak clad temperature values for the tests of group 3.Figure 8
Peak clad temperature values for the tests of group 4.Figure 9
Peak clad temperature values for the tests of group 5.In general, EUREKA-2/RR code is shown to provide conservative estimates of peak power and also of peak clad temperature values which in turn indicates whether the model developed is able to accurately represent the physical process involved in RIA scenarios of SPERT IV. Various input parameters, say, DNB correlation, kinetic parameters, and feedback coefficients, or the assumptions or misinterpretation of specifications considered during modeling or any limitations of code as well need to be examined seriously whether they cause effects in modeling such RIA tests.


## 5. Conclusion

As a part of validation, SPERT IV reactor model is developed to simulate the RIA (reactivity initiated accident) transients. The results that represent the state of modeling do not allow concluding that it is the best model or EUREKA-2/RR is the best code to model such RIA tests of SPERT IV. On the contrary, it is to say that validating the code is a continuous process that is worth pursuing in order to improve the model with an aim of obtaining the best simulation results. To reduce the difference between calculated and experimental values, further efforts then must be paid. More other benchmark cases of SPERT (or others) could be conducted from where suggestions might come to modify the code that could lead the EUREKA-2/RR code to be a more useful tool for research reactor transient analysis.



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*Source: 167426-2014-12-09.xml*