# Subchannel Analysis of Wire Wrapped SCWR Assembly

Authors: Jianqiang Shan; Henan Wang; Wei Liu; Linxing Song; Xuanxiang Chen; Yang Jiang
Journal: Science and Technology of Nuclear Installations
 (2014)

---

## Abstract

Application of wire wrap spacers in SCWR can reduce pressure drop and obtain better mixing capability. As a consequence, the required coolant pumping power is decreased and the coolant temperature profile inside the fuel bundle is flattened which will obviously decrease the peak cladding temperature. The distributed resistance model for wire wrap was developed and implemented in ATHAS subchannel analysis code. The HPLWR wire wrapped assembly was analyzed. The results show that: (1) the assembly with wire wrap can obtain a more uniform coolant temperature profile than the grid spaced assembly, which will result in a lower peak cladding temperature; (2) the pressure drop in a wire wrapped assembly is less than that in a grid spaced assembly, which can reduce the operating power of pump effectively; (3) the wire wrap pitch has significant effect on the flow in the assembly. SmallerH
w
i
r
e
/
D
r
o
d will result in stronger cross flow a more uniform coolant temperature profile, and also a higher pressure drop.


---

## Body

## 1. Introduction

The supercritical water-cooled reactor (SCWR) is essentially a water reactor operating above the thermodynamic critical point of water (Pc = 22.064 MPa). It is considered as one of the most promising Generation IV reactors because of its simplicity, high thermal efficiency, and nearly fifty years of industrial experience from thermal-power stations with a SCW cycle [1]. Evolving from the existing designs, there are currently two types of SCWR concepts [2]: (a) a large reactor pressure vessel containing the reactor core (fuelled) heat source, analogous to conventional PWRs and BWRs, and (b) distributed pressure tubes or channels containing fuel bundles, analogous to conventional CANDU and RBMK nuclear reactors. The arrangement of separated moderator (moderator box in pressure vessel type and heavy water moderator in calandria in pressure tube type) is applied in each design, due to the sharp change in the thermal properties of coolant near the pseudo-critical point.To obtain a small water volume fraction in core, tight lattices are necessary. Wire wrap spacers, an alternative to grid spacers, have been used extensively in LMFBR [3] and tight-lattice high-conversion cores [4], mainly due to their advantageous pressure drop and better mixing capability. As a consequence, the required coolant pumping power is decreased and the coolant temperature profile inside the fuel bundle is flattened which will obviously decrease the peak cladding temperature. The other potential advantage of wire wrap spacer is that it can improve the heat transfer at the rod gap where heat transfer deterioration occurs in SCWR assembly. For SCWR design, wire wrapped assembly has been selected in both three-pass HPLWR [5] and US SCWR [6].The influence of wire wrap under supercritical pressure conditions should be well studied. Himmel et al. [7] studied the mixing coefficients for a subchannel flow through a HPLWR fuel assembly with 40 wire wrapped fuel pins in a square arrangement, and their analyses were concentrated on a section of 3 subchannels between the assembly box and the inner moderator box walls. Laurien et al. [8] carried out the heat transfer experiments with a 10 mm rod inside a square vertical channel with a wire wrapped helically around it. The results showed that, based on the comparison with an identical channel without the helical wrapped wire, the wire spacer did not enhance the heat transfer significantly under normal heat transfer conditions but helped improve the heat transfer in the pseudo-critical region and shift the onset of the deterioration to downstream. Chandra et al. [9] analyzed the wire wrap effect with CFD method. The results showed that the adiabatic helical wire wrap around the inner heated cylinder of the annulus prevented the heat transfer deterioration from occurring in the considered test case, even at very high heat fluxes. This was related to the enhanced production of the turbulent kinetic energy by the presence of helical wire wrap, which increased the turbulent mixing effect and consequently the heat transfer and finally reduced the wall temperature.To better understand the behavior of the coolant and cladding under the influence of wire wrap in the whole assembly, subchannel analysis is an effective and simpler method. The present paper developed a subchannel code for wire wrapped SCWR bundle based on the ATHAS code.


## 2. Model Description

### 2.1. Basic Conservation Equations of ATHAS

The basic equations of the mathematical model [10] are derived by applying the general equations of continuity, energy, and momentum to a subchannel i control volume j. The equations are as follows.Mass. Consider
(1)
A
¯
∂
∂
t
〈
〈
ρ
〉
〉
V
+
∂
∂
Z
(
〈
ρ
u
〉
A
A
)
+
∑
k
=
1
n
k
(
〈
ρ
V
k
〉
s
S
)
k
=
0
,
where the density, the axial mass flux, and the lateral mass flux are defined by
(2)
〈
〈
ρ
〉
〉
V
=
1
V
∫
V
ρ
d
V
,
〈
ρ
u
〉
A
=
1
A
∫
A
ρ
u
d
A
,
〈
ρ
v
〉
A
=
1
A
∫
A
ρ
v
d
A
.The first term is the time rate of change of mass per unit axial length and the second is spatial variation in axial mass flux per unit length. The last term is the sum on all gap connections of the lateral mass flux per unit length which is the cross flow associated with subchannel analysis.Energy. Consider
(3)
A
¯
∂
∂
t
〈
〈
ρ
h
〉
〉
V
+
∂
∂
Z
〈
ρ
h
u
〉
A
A
+
∑
k
=
1
n
k
[
〈
ρ
h
V
k
〉
S
S
]
k
=
∑
r
=
1
n
r
[
P
r
Φ
j
H
r
(
t
r
-
t
f
)
]
r
+
∑
W
=
1
n
W
[
L
W
H
W
(
t
W
-
t
f
)
]
W
+
∂
∂
Z
A
〈
k
f
∂
t
∂
Z
〉
A
-
∑
k
=
1
n
k
[
S
·
C
g
k
f
L
c
(
t
i
-
t
j
)
]
k
-
∑
k
=
1
n
k
[
W
′
(
h
i
′
-
h
j
′
)
]
k
.The equation considers the heat transfer from the rod and wall-to-channel (if necessary) to the control volume, the axial fluid heat conduction, the lateral fluid heat conduction through the gap between two channels, and turbulent energy input.Axial Momentum. Consider
(4)
A
¯
∂
∂
t
〈
〈
ρ
u
〉
〉
V
+
∂
∂
Z
〈
ρ
u
2
〉
A
A
+
∑
k
=
1
n
k
[
〈
ρ
V
k
u
〉
S
S
]
k
=
-
A
¯
∂
∂
Z
〈
p
〉
A
-
1
2
(
f
D
e
+
C
Δ
Z
)
〈
ρ
u
2
〉
A
A
-
g
A
¯
〈
〈
ρ
〉
〉
V
cos
⁡
θ
-
C
T
∑
k
=
1
n
k
[
W
′
(
u
t
′
-
u
f
′
)
]
k
.The first term at the left side is the time rate of change of momentum per unit axial length and the second and third are the spatial variation in axial momentum per unit length. The four terms at right side are the total pressure force on the control volume, axial drag force, the gravity force, and the force due to turbulent mixing, respectively.Lateral Momentum. Consider
(5)
C
S
{
∑
k
=
1
n
k
[
〈
ρ
V
k
〉
S
S
l
cos
⁡
Δ
β
]
k
,
j
-
∑
k
=
1
n
k
[
〈
ρ
V
k
〉
S
S
l
cos
⁡
Δ
β
]
k
,
i
}
+
∂
∂
t
〈
〈
ρ
V
k
〉
〉
V
′
S
+
∂
∂
Z
〈
ρ
u
V
k
〉
A
′
S
=
b
l
(
〈
p
〉
A
,
i
-
〈
p
〉
A
,
j
)
-
1
2
S
l
k
G
〈
ρ
V
k
2
〉
S
-
g
〈
〈
ρ
〉
〉
V
′
S
sin
⁡
θ
cos
⁡
⁡
β
.The first term at the left side is the net lateral momentum flux and the factorC
s is included to help account for the imperfect coupling between communicating gaps. The second and third terms at the left side are the time rate of change of lateral momentum per unit lateral length and spatial variation in lateral momentum per unit length. The three terms at the right side are the pressure difference between adjacent channels, the total drag force, and the gravity force, respectively.The constitutive correlations selected in the analysis are shown as follows based on Shan et al.’s work [10].Friction coefficient: Blasius correlation [11] for single phase turbulent flow:
(6)
f
=
0.3164
Re
-
0.25
.Heat transfer coefficient: Bishop correlation (1964) [12] for supercritical water:
(7)
N
u
x
=
0.0069
Re
x
0.9
Pr
¯
x
0.66
(
ρ
w
ρ
b
)
x
0.43
(
1
+
2.4
D
x
)
.Turbulent mixing factor: Rowe and Angle correlation [13] in the bundle condition:
(8)
β
=
0.021
·
Re
-
0.1
.The selection of Blasius correlation, Bishop correlation (1964), and Rowe and Angle correlation in this paper can obtain relatively high maximum cladding surface temperature and present more conservative estimate.The code has been validated under supercritical pressure condition [14] and successfully applied in the analysis of pressure vessel and pressure tube type SCWR bundle [10, 15, 16].


### 2.2. Wire Wrap Model

Hydraulic resistance model which was initially proposed by Ninokata et al. [17] is developed to account for the existence of the wire wrap spacer in rod bundle. These models are of ‘‘distributed resistance’’ type and add flow resistance term into the axial and transverse momentum equations as a function of subchannel geometry and flow velocity. The models are general enough to cover a wide range of geometrical parameters, wire position, and flow regime.In the subchannel formulation, it is a common practice to assume three types of control volume for (1) mass and energy balance, (2) lateral momentum balance, and (3) axial momentum balance. Figure1 illustrates the typical mass and energy balance control volume (ABCDEF-LMNJPQ) and lateral momentum control volume (SPTUKV-GYZWOX). Note that the control volume for the axial momentum balance is staggered in the axial direction with respect to the energy and mass balance control volume.Figure 1
Three-dimensional view of a subchannel and a gap with wire wrap.In this study, focus is mainly placed on the momentum balance conservation equation, that is, (4) and (5).The second terms at the right side of (4) and (5) represent the momentum exchange between the solid surface and the fluid. These terms, which are the forces exerted on the fluid by the wall, are replaced with the distributed resistance terms. These terms for the rod bundles with wire wraps can be divided into four components, as shown in Figure 2. These forces of F
R
L and F
W
N are estimated by correlations depending on the direction of the dominant flow. Each force can be written as
(9)
F
R
A
=
R
(
c
)
(
A
R
A
w
′′
)
cos
⁡
⁡
α
,
F
W
T
=
R
(
c
)
(
1
-
A
R
A
W
′′
)
cos
⁡
⁡
(
φ
-
α
)
,
where
(10)
R
(
c
)
=
A
W
′′
f
M
(
c
)
8
ρ
c
|
c
|
c
2
=
u
2
+
v
2
.Component of the drag forces and velocities in a wire wrapped rod.
(a)
(b)For the predominantly axial flow,(11)
F
R
L
=
A
W
′′
f
G
8
ρ
|
v
|
v
(
D
V
′′
S
T
)
0.4
(
S
L
S
T
)
0.6
,
F
W
N
=
A
W
P
f
n
2
ρ
|
v
k
|
v
k
,
where f
G is a friction factor based on the cross flow Reynolds number, S
T is the rod pitch, and S
L is the distance between two rods in a transverse row (Figure 3).Figure 3
Average wire wrap position and gap definition.The hydraulic resistance per unit volume for the solution of the axial and lateral momentum equations, respectively, can be represented as follows:(12)
1
2
(
f
D
e
+
C
Δ
Z
)
〈
ρ
u
2
〉
A
A
=
F
R
A
+
F
W
T
cos
⁡
⁡
φ
+
F
W
N
sin
⁡
φ
,
1
2
S
l
k
G
〈
ρ
V
k
2
〉
S
=
F
R
L
+
F
W
T
sin
⁡
φ
-
F
W
N
cos
⁡
⁡
φ
.


## 2.1. Basic Conservation Equations of ATHAS

The basic equations of the mathematical model [10] are derived by applying the general equations of continuity, energy, and momentum to a subchannel i control volume j. The equations are as follows.Mass. Consider
(1)
A
¯
∂
∂
t
〈
〈
ρ
〉
〉
V
+
∂
∂
Z
(
〈
ρ
u
〉
A
A
)
+
∑
k
=
1
n
k
(
〈
ρ
V
k
〉
s
S
)
k
=
0
,
where the density, the axial mass flux, and the lateral mass flux are defined by
(2)
〈
〈
ρ
〉
〉
V
=
1
V
∫
V
ρ
d
V
,
〈
ρ
u
〉
A
=
1
A
∫
A
ρ
u
d
A
,
〈
ρ
v
〉
A
=
1
A
∫
A
ρ
v
d
A
.The first term is the time rate of change of mass per unit axial length and the second is spatial variation in axial mass flux per unit length. The last term is the sum on all gap connections of the lateral mass flux per unit length which is the cross flow associated with subchannel analysis.Energy. Consider
(3)
A
¯
∂
∂
t
〈
〈
ρ
h
〉
〉
V
+
∂
∂
Z
〈
ρ
h
u
〉
A
A
+
∑
k
=
1
n
k
[
〈
ρ
h
V
k
〉
S
S
]
k
=
∑
r
=
1
n
r
[
P
r
Φ
j
H
r
(
t
r
-
t
f
)
]
r
+
∑
W
=
1
n
W
[
L
W
H
W
(
t
W
-
t
f
)
]
W
+
∂
∂
Z
A
〈
k
f
∂
t
∂
Z
〉
A
-
∑
k
=
1
n
k
[
S
·
C
g
k
f
L
c
(
t
i
-
t
j
)
]
k
-
∑
k
=
1
n
k
[
W
′
(
h
i
′
-
h
j
′
)
]
k
.The equation considers the heat transfer from the rod and wall-to-channel (if necessary) to the control volume, the axial fluid heat conduction, the lateral fluid heat conduction through the gap between two channels, and turbulent energy input.Axial Momentum. Consider
(4)
A
¯
∂
∂
t
〈
〈
ρ
u
〉
〉
V
+
∂
∂
Z
〈
ρ
u
2
〉
A
A
+
∑
k
=
1
n
k
[
〈
ρ
V
k
u
〉
S
S
]
k
=
-
A
¯
∂
∂
Z
〈
p
〉
A
-
1
2
(
f
D
e
+
C
Δ
Z
)
〈
ρ
u
2
〉
A
A
-
g
A
¯
〈
〈
ρ
〉
〉
V
cos
⁡
θ
-
C
T
∑
k
=
1
n
k
[
W
′
(
u
t
′
-
u
f
′
)
]
k
.The first term at the left side is the time rate of change of momentum per unit axial length and the second and third are the spatial variation in axial momentum per unit length. The four terms at right side are the total pressure force on the control volume, axial drag force, the gravity force, and the force due to turbulent mixing, respectively.Lateral Momentum. Consider
(5)
C
S
{
∑
k
=
1
n
k
[
〈
ρ
V
k
〉
S
S
l
cos
⁡
Δ
β
]
k
,
j
-
∑
k
=
1
n
k
[
〈
ρ
V
k
〉
S
S
l
cos
⁡
Δ
β
]
k
,
i
}
+
∂
∂
t
〈
〈
ρ
V
k
〉
〉
V
′
S
+
∂
∂
Z
〈
ρ
u
V
k
〉
A
′
S
=
b
l
(
〈
p
〉
A
,
i
-
〈
p
〉
A
,
j
)
-
1
2
S
l
k
G
〈
ρ
V
k
2
〉
S
-
g
〈
〈
ρ
〉
〉
V
′
S
sin
⁡
θ
cos
⁡
⁡
β
.The first term at the left side is the net lateral momentum flux and the factorC
s is included to help account for the imperfect coupling between communicating gaps. The second and third terms at the left side are the time rate of change of lateral momentum per unit lateral length and spatial variation in lateral momentum per unit length. The three terms at the right side are the pressure difference between adjacent channels, the total drag force, and the gravity force, respectively.The constitutive correlations selected in the analysis are shown as follows based on Shan et al.’s work [10].Friction coefficient: Blasius correlation [11] for single phase turbulent flow:
(6)
f
=
0.3164
Re
-
0.25
.Heat transfer coefficient: Bishop correlation (1964) [12] for supercritical water:
(7)
N
u
x
=
0.0069
Re
x
0.9
Pr
¯
x
0.66
(
ρ
w
ρ
b
)
x
0.43
(
1
+
2.4
D
x
)
.Turbulent mixing factor: Rowe and Angle correlation [13] in the bundle condition:
(8)
β
=
0.021
·
Re
-
0.1
.The selection of Blasius correlation, Bishop correlation (1964), and Rowe and Angle correlation in this paper can obtain relatively high maximum cladding surface temperature and present more conservative estimate.The code has been validated under supercritical pressure condition [14] and successfully applied in the analysis of pressure vessel and pressure tube type SCWR bundle [10, 15, 16].


## 2.2. Wire Wrap Model

Hydraulic resistance model which was initially proposed by Ninokata et al. [17] is developed to account for the existence of the wire wrap spacer in rod bundle. These models are of ‘‘distributed resistance’’ type and add flow resistance term into the axial and transverse momentum equations as a function of subchannel geometry and flow velocity. The models are general enough to cover a wide range of geometrical parameters, wire position, and flow regime.In the subchannel formulation, it is a common practice to assume three types of control volume for (1) mass and energy balance, (2) lateral momentum balance, and (3) axial momentum balance. Figure1 illustrates the typical mass and energy balance control volume (ABCDEF-LMNJPQ) and lateral momentum control volume (SPTUKV-GYZWOX). Note that the control volume for the axial momentum balance is staggered in the axial direction with respect to the energy and mass balance control volume.Figure 1
Three-dimensional view of a subchannel and a gap with wire wrap.In this study, focus is mainly placed on the momentum balance conservation equation, that is, (4) and (5).The second terms at the right side of (4) and (5) represent the momentum exchange between the solid surface and the fluid. These terms, which are the forces exerted on the fluid by the wall, are replaced with the distributed resistance terms. These terms for the rod bundles with wire wraps can be divided into four components, as shown in Figure 2. These forces of F
R
L and F
W
N are estimated by correlations depending on the direction of the dominant flow. Each force can be written as
(9)
F
R
A
=
R
(
c
)
(
A
R
A
w
′′
)
cos
⁡
⁡
α
,
F
W
T
=
R
(
c
)
(
1
-
A
R
A
W
′′
)
cos
⁡
⁡
(
φ
-
α
)
,
where
(10)
R
(
c
)
=
A
W
′′
f
M
(
c
)
8
ρ
c
|
c
|
c
2
=
u
2
+
v
2
.Component of the drag forces and velocities in a wire wrapped rod.
(a)
(b)For the predominantly axial flow,(11)
F
R
L
=
A
W
′′
f
G
8
ρ
|
v
|
v
(
D
V
′′
S
T
)
0.4
(
S
L
S
T
)
0.6
,
F
W
N
=
A
W
P
f
n
2
ρ
|
v
k
|
v
k
,
where f
G is a friction factor based on the cross flow Reynolds number, S
T is the rod pitch, and S
L is the distance between two rods in a transverse row (Figure 3).Figure 3
Average wire wrap position and gap definition.The hydraulic resistance per unit volume for the solution of the axial and lateral momentum equations, respectively, can be represented as follows:(12)
1
2
(
f
D
e
+
C
Δ
Z
)
〈
ρ
u
2
〉
A
A
=
F
R
A
+
F
W
T
cos
⁡
⁡
φ
+
F
W
N
sin
⁡
φ
,
1
2
S
l
k
G
〈
ρ
V
k
2
〉
S
=
F
R
L
+
F
W
T
sin
⁡
φ
-
F
W
N
cos
⁡
⁡
φ
.


## 3. Results and Analysis

### 3.1. Description of HPLWR Assembly

The high performance light water reactor (HPLWR) is funded by the European Commission. A specific core design proposed by Schulenberg et al. [18] assumes that the coolant is guided three times through the core during its heat-up from 280°C to 500°C at a system pressure of 25 MPa. Figure 4 illustrates the HPLWR assembly configuration. Fischer et al. [5] gave the detailed design as follows: the assembly cluster is built with nine assemblies and with a gap of 10 mm between the boxes; a total number of 40 fuel rods per assembly with 8 mm outer cladding diameter at a pitch of 9.44 mm are housed within a stainless steel box of 2.5 mm wall thickness and 72.5 mm outer size; a single wire of 1.34 mm diameter is wrapped around each fuel rod with an axial pitch of 200 mm, leaving a tolerance of 0.1 mm between the wire and the fuel rods or the box walls, respectively; the inner moderator box has an outer size of 26.9 mm and a wall thickness of 0.8 mm, which is made from stainless steel as well; the active core height is assumed to be 4.2 m and the total length of the fuel rods is considered as 4.71 m if the fission gas plenum is included. Figure 4 shows the subchannel and fuel identification in a HPLWR fuel bundle. Totally 60 subchannels, 40 rods, and 2 conducting walls are defined here. The heat transfer between the subchannels and moderator box/assembly gap is also considered with conducting wall model in the ATHAS code.Figure 4
Fuel assembly design and subchannel identification.Table1 lists the geometry of the assembly and Table 2 gives the operating parameters. Figure 5 shows the relative axial power distribution, which is the result of neutronic/thermal-hydraulics coupling analysis [19]. The radial power distribution is assumed as uniform.Table 1
Fuel assembly geometry parameters.
Parameters
Values
Fuel rod outer diameter
8.00 mm
Fuel rod pitch
9.44 mm
Pitch/diameter ratio (P
/
D)
1.18
Active height
4200 cm
Total height
4710 cm
Wire diameter
1.34 mm
Wire pitch
200 mm
Moderator box length
26.9 mm
Moderator box wall thickness
0.8 mm
Outside box length
72.5 mm
Outside box wall thickness
2.5 mm
Gap between fuel rod and box wall
1.43 mm
0.5 gap around one fuel assembly
5.0 mmTable 2
Reactor operation parameters and correlations options in current analysis.
Parameters
Values
Coolant inlet pressure
25 MPa
Coolant inlet temperature
280°C
Coolant exit temperature
500°C
Average heat flux
0.6142 MW·m−2
Mass flux
780 kg·m−2·s−1Figure 5
Relative power distribution.


### 3.2. Subchannel Analysis Results with Wire Wrapped and Grid Spaced Assemblies

To compare with the behavior of wire wrap in the SCWR assembly, a subchannel analysis of assembly with grid space is also taken. The parameters of grid spacers are given by Cheng et al. [20]. There are 15 grid spacers along the axial lengths.The comparison of axial cladding temperature profiles in the hot channel between wire wrapped and grid spaced assemblies is shown in Figure6. The peak cladding temperature is 587.6°C for wire wrapped assembly and 603.5°C for grid spaced assembly, respectively. The location of peak cladding temperature is at subchannel 43, rod 25, and 3.96 m at axial position. The reason for the temperature difference is that more forced cross flow between subchannels, result in a more uniform coolant temperature profile. Figure 7 shows the coolant temperature profile in the subchannels at the axial position where the peak cladding temperature occurs. The difference of coolant temperature between the hottest and coldest channels is 25.3°C for the wire wrap and 40.2°C for the grid spacer, respectively. Figure 8 shows the pressure drop in the two kinds of assembly; it can be observed that the pressure loss in the wire wrapped assembly is less than that in the grid spaced assembly, which consequently can reduce the required pump power.Figure 6
Axial cladding temperature profile in the hot channel.Figure 7
Coolant temperature profile at axial position where the peak cladding temperature occurs.Figure 8
Pressure drop of two kinds of assembly.


### 3.3. Sensitivity Analysis of Wire Wrap Pitch

Sensitivity analysis of wire wrap pitch was also studied. The pitch is selected according to the criteria determined by Diller [21], H
wire
/
D
rod
<
50. So four H
wire
/
D
rod values have been selected for analysis, which are H
wire
/
D
rod
=
20,30,40, and 50, respectively.Figure9 shows the comparison of exit cooling temperature profiles with different H
wire
/
D
rod values. It is found that lower H
wire
/
D
rod will result in a more uniform profile, since the temperature difference between the hottest and coldest channels is 60.9°C for H
wire
/
D
rod
=
50 and 21.9°C for H
wire
/
D
rod
=
20. This is understandable because lower H
wire
/
D
rod causes more cross flow. However, lower H
wire
/
D
rod also leads to a higher pressure drop, as shown in Figure 10. The pressure drop is increased from 51.8 kPa for H
wire
/
D
rod
=
50 to 56.1 kPa for H
wire
/
D
rod
=
20.Figure 9
Exit cooling temperature profile with differentH
wire
/
D
rod values.Figure 10
Pressure drop value with differentH
wire
/
D
rod.Figure11 shows the peak cladding temperature comparison with different H
wire
/
D
rod values. As we have discussed before, the peak cladding temperature mainly depends on whether the coolant temperature profile in subchannels is uniform or not. Higher H
wire
/
D
rod will result in a higher cladding temperature. As for H
wire
/
D
rod
=
50, the calculated peak cladding temperature is 603.3°C, nearly the same as grid spaced assembly.Figure 11
The peak cladding temperature comparison with differentH
wire
/
D
rod values.


## 3.1. Description of HPLWR Assembly

The high performance light water reactor (HPLWR) is funded by the European Commission. A specific core design proposed by Schulenberg et al. [18] assumes that the coolant is guided three times through the core during its heat-up from 280°C to 500°C at a system pressure of 25 MPa. Figure 4 illustrates the HPLWR assembly configuration. Fischer et al. [5] gave the detailed design as follows: the assembly cluster is built with nine assemblies and with a gap of 10 mm between the boxes; a total number of 40 fuel rods per assembly with 8 mm outer cladding diameter at a pitch of 9.44 mm are housed within a stainless steel box of 2.5 mm wall thickness and 72.5 mm outer size; a single wire of 1.34 mm diameter is wrapped around each fuel rod with an axial pitch of 200 mm, leaving a tolerance of 0.1 mm between the wire and the fuel rods or the box walls, respectively; the inner moderator box has an outer size of 26.9 mm and a wall thickness of 0.8 mm, which is made from stainless steel as well; the active core height is assumed to be 4.2 m and the total length of the fuel rods is considered as 4.71 m if the fission gas plenum is included. Figure 4 shows the subchannel and fuel identification in a HPLWR fuel bundle. Totally 60 subchannels, 40 rods, and 2 conducting walls are defined here. The heat transfer between the subchannels and moderator box/assembly gap is also considered with conducting wall model in the ATHAS code.Figure 4
Fuel assembly design and subchannel identification.Table1 lists the geometry of the assembly and Table 2 gives the operating parameters. Figure 5 shows the relative axial power distribution, which is the result of neutronic/thermal-hydraulics coupling analysis [19]. The radial power distribution is assumed as uniform.Table 1
Fuel assembly geometry parameters.
Parameters
Values
Fuel rod outer diameter
8.00 mm
Fuel rod pitch
9.44 mm
Pitch/diameter ratio (P
/
D)
1.18
Active height
4200 cm
Total height
4710 cm
Wire diameter
1.34 mm
Wire pitch
200 mm
Moderator box length
26.9 mm
Moderator box wall thickness
0.8 mm
Outside box length
72.5 mm
Outside box wall thickness
2.5 mm
Gap between fuel rod and box wall
1.43 mm
0.5 gap around one fuel assembly
5.0 mmTable 2
Reactor operation parameters and correlations options in current analysis.
Parameters
Values
Coolant inlet pressure
25 MPa
Coolant inlet temperature
280°C
Coolant exit temperature
500°C
Average heat flux
0.6142 MW·m−2
Mass flux
780 kg·m−2·s−1Figure 5
Relative power distribution.


## 3.2. Subchannel Analysis Results with Wire Wrapped and Grid Spaced Assemblies

To compare with the behavior of wire wrap in the SCWR assembly, a subchannel analysis of assembly with grid space is also taken. The parameters of grid spacers are given by Cheng et al. [20]. There are 15 grid spacers along the axial lengths.The comparison of axial cladding temperature profiles in the hot channel between wire wrapped and grid spaced assemblies is shown in Figure6. The peak cladding temperature is 587.6°C for wire wrapped assembly and 603.5°C for grid spaced assembly, respectively. The location of peak cladding temperature is at subchannel 43, rod 25, and 3.96 m at axial position. The reason for the temperature difference is that more forced cross flow between subchannels, result in a more uniform coolant temperature profile. Figure 7 shows the coolant temperature profile in the subchannels at the axial position where the peak cladding temperature occurs. The difference of coolant temperature between the hottest and coldest channels is 25.3°C for the wire wrap and 40.2°C for the grid spacer, respectively. Figure 8 shows the pressure drop in the two kinds of assembly; it can be observed that the pressure loss in the wire wrapped assembly is less than that in the grid spaced assembly, which consequently can reduce the required pump power.Figure 6
Axial cladding temperature profile in the hot channel.Figure 7
Coolant temperature profile at axial position where the peak cladding temperature occurs.Figure 8
Pressure drop of two kinds of assembly.


## 3.3. Sensitivity Analysis of Wire Wrap Pitch

Sensitivity analysis of wire wrap pitch was also studied. The pitch is selected according to the criteria determined by Diller [21], H
wire
/
D
rod
<
50. So four H
wire
/
D
rod values have been selected for analysis, which are H
wire
/
D
rod
=
20,30,40, and 50, respectively.Figure9 shows the comparison of exit cooling temperature profiles with different H
wire
/
D
rod values. It is found that lower H
wire
/
D
rod will result in a more uniform profile, since the temperature difference between the hottest and coldest channels is 60.9°C for H
wire
/
D
rod
=
50 and 21.9°C for H
wire
/
D
rod
=
20. This is understandable because lower H
wire
/
D
rod causes more cross flow. However, lower H
wire
/
D
rod also leads to a higher pressure drop, as shown in Figure 10. The pressure drop is increased from 51.8 kPa for H
wire
/
D
rod
=
50 to 56.1 kPa for H
wire
/
D
rod
=
20.Figure 9
Exit cooling temperature profile with differentH
wire
/
D
rod values.Figure 10
Pressure drop value with differentH
wire
/
D
rod.Figure11 shows the peak cladding temperature comparison with different H
wire
/
D
rod values. As we have discussed before, the peak cladding temperature mainly depends on whether the coolant temperature profile in subchannels is uniform or not. Higher H
wire
/
D
rod will result in a higher cladding temperature. As for H
wire
/
D
rod
=
50, the calculated peak cladding temperature is 603.3°C, nearly the same as grid spaced assembly.Figure 11
The peak cladding temperature comparison with differentH
wire
/
D
rod values.


## 4. Conclusion and Discussion

The subchannel code ATHAS is modified with distributed resistance model to meet the demand of wire wrapped SCWR assembly. Conclusions can be concluded as follows.(1)
The assembly with wire wrap can obtain a more uniform coolant temperature profile than the grid spaced assembly, which will result in a lower peak cladding temperature.
(2)
The pressure drop in a wire wrapped assembly is less than that in a grid spaced assembly, which can reduce the operating power of pump effectively.
(3)
The wire wrap pitch has significant effect on the flow in the assembly. SmallerH
wire
/
D
rod will result in stronger cross flow, a more uniform coolant temperature profile, and also a higher pressure drop.Although the feasibility of wire wrapped assembly from the thermal-hydraulic point of view is approved in this work, the flow-induced vibration induced by wire wrap still needs further study.



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*Source: 301052-2014-02-23.xml*