# Power Level Control of Nuclear Power Plant Based on Asymptotical State Observer under Neutron Sensor Fault

Authors: Liming Zhang; Hongyun Xie; Qizhi Duan; Chao Lu; Jixue Li; Zhihong Lv
Journal: Science and Technology of Nuclear Installations
 (2021)

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## Abstract

Power level control is one of the critical functions in the instrument and control system of nuclear power plants (NPPs). In most power level control systems of NPPs, the power level or average neutron flux in reactor cores provided by out-of-core neutron sensors are usually measured as feedback of power control systems, while, as critical measuring devices, there is a risk of damage to out-of-core neutron sensors. For improving the operation reliability of NPPs under the neutron sensors’ failure, a power control system based on power observer is developed in this work. The simulation based on NPP simulator shows the power control system based on the observer is effective when neutron sensors fail.


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## Body

## 1. Introduction

Ensuring safe and effective operations of nuclear power plants (NPPs) is the precondition during the development [1]. In terms of reactor power control, the implementation of desirable control for a core in an NPP is an important measure to improve security and effectiveness of the core.In most power control systems of NPPs, the average neutron flux in reactor cores provided by out-of-core neutron sensors is usually measured as feedback of power control systems, which can be shown as Figure1 [2]. During the past decades, some core power control methods are developed gradually, including optimal control [3, 4], neural network [5–7], fuzzy logical control [8], slide mode control [9, 10], model predictive control [11–13], and fractional order control [14, 15]. These control methods have to depend on the neutron flux measurement, while, as critical measuring devices, there is a risk of damage to out-of-core neutron sensors [16]. The neutron sensors are difficult to be replaced and maintained online. If neutron sensors fail, the power control system cannot work normally, and NPPs will be shut down further. On the contrary, the thermocouple in the secondary loop is convenient for replacement and maintenance. Meanwhile, the coolant temperature in secondary can also reflect the core power level. Therefore, it is possible to rebuild the neutron flux and core power level according to the coolant temperature in the secondary loop, when the out-of-core neutron sensors fail.Figure 1
The structure of power level control system in NPP.For improving the operation reliability of NPPs under the neutron sensors’ failure, a power control system based on power observer is developed in this work. Firstly, a common NPP dynamic model containing neutron kinetic and thermal-hydraulic is built, and then the formulation of control problem about power level control under neutron sensors’ failure is presented; after that, based on the separation principle, the power level observer and power level controller are developed independently; at last, the effectiveness of the power level controller based on the observer is verified.


## 2. Modeling

As shown in Figure2, the whole plant module of NPPs is mainly composed of a reactor core with thermal neutron, pressurized water, U-tube steam generator (UTSG), main pump, necessary connection pipes, and vessels [17]. Since this study focuses on modeling the dynamic response and sensors fault characteristics between the nuclear reactor power and primary coolant as well as proposing a proper control method under the neutron sensors fault to enhance the reliability of the control system, it is reasonable to adopt a simplified model of the lumped parameters core, coolant, and UTSG module, where the corresponding nodalization scheme is shown in Figure 2.Figure 2
Nodalization scheme of the whole plant module of NPPs.


### 2.1. Neutron Kinetic

According to the lumped parameter method, the nonlinear core model is established via using the point kinetics equations with six groups of delayed neutrons and two reactivity feedback mechanisms [18]. The normalized point kinetics equations for the critical core without external source of neutrons can be expressed as(1)dntdt=δt−βΛ+∑i=16λicit+qt,dcitdt=βiΛnt−λicit,i=1,2,…,6.The reactivity feedbacks in this model are expressed as a function of the average temperatures of fuel and coolant. As a result, the total reactivity is the control rod reactivity combined with the feedbacks described as(2)δt=δrod+αfTf−Tf0+αcoolantTp−Tp0,where the subscript 0 refers to a reference condition, taken at the rated power, n means the neutron density, ρ means the reactivity, β means the neutron fraction, Λ means the neutron generation time, λi means the decay constant of ith group, ci means the delayed neutron precursor concentration of ith group, δrod means the reactivity of rod, αf means the reactivity feedback of fuel, αcoolant means the reactivity feedback of coolant in reactor core, Tf means the temperature of fuel, Tf means the temperature of fuel at the rated power, and Tp means the average temperature of pressurized water of reactor core.It is assumed that the neutron density in steady state isn0, delayed neutron precursor concentration of ith group in steady state is ci0, and then the neutron kinetic model can be linearized as follows:(3)dΔntdt=δ0−βΛΔnt+n0ΛΔδt+∑i=16λiΔcit,dΔcitdt=βiΛΔnt−λiΔcit,where Δ means the increment.


### 2.2. Thermal-Hydraulic

#### 2.2.1. Core

The reactor core is assumed to be a lumped cylindrical area as a function of the power [19]. The fission energy is released in the fuel elements in the form of heat. This heat is then transferred to the upcoming pressurized water. This process is described as follows:(4)ρfVfCfdTfdt=P−UtAcTf−Tc,(5)ρcVcCpdTcdt=UtAcTf−Tc−GpCpTcout−Tcin,where ρf and ρc mean the fuel density and the primary coolant density in the reactor core, respectively, Vf means the fuel volume, P means the reactor power, Ut means the heat transfer coefficient between fuel and primary coolant, Ac means the fuel assemblies area, Cf and Cp the mean specific enthalpy of fuel and primary coolant, respectively, Tf and Tc mean fuel and primary coolant temperatures, respectively, and Gp means the mass flow rate of primary loop.Accordingly, the increment form of equations (4) and (5) can be given as(6)ρfVfCfdΔTfdt=ΔP−UtAcΔTf−ΔTc,ρcVcCpdΔTcdt=UtAcΔTf−ΔTc−GpCpΔTcout−ΔTcin.


#### 2.2.2. Steam Generator

Usually, steam generators in NPPs will be of U-tubes and counter current type. Single-phase pressurized water and two-phase water are in shell-side and tube-side of USTGs, respectively. In order to give a simple description for the control-oriented modeling, one-section model is adopted to describe the main thermodynamics of UTSGs:(7)ρsgpVsgpCpdTsgpdt=GpCpTsgpin−Tsgpout−UsgAsgTsgΔ,(8)ρsgsVsgsdTsgsdt=GsCsTfw−Tsgsout+UsgAsgTsgΔ,where Tsgp means the average coolant temperature in the primary side of UTSGs, Tsgpin and Tsgpout mean inlet and outlet coolant temperatures in the primary side of UTSGs, TsgΔ means the temperature difference between the coolant flows in the two sides of UTSGs, which can be given by TsgΔ=Tsgp−Tsgs, where Tsgp and Tsgs mean average coolant temperatures in primary and secondary sides of UTSGs, respectively, Tfw means the feedwater temperature, Tsgsout means the outlet temperature in secondary side of UTSGs, Usg and Asg mean the heat transfer coefficient and area between the two sides of UTSGs, respectively, and Vsgp and Vsgs mean primary and secondary side volume of UTSGs, respectively.Accordingly, the increment form of equations (7) and (8) can be given as(9)ρsgpVsgpCpdΔTsgpdt=GpCpΔTsgpin−ΔTsgpout−UsgAsgΔTsgΔ,ρsgsVsgsCsdΔTsgsdt=GsCsΔTfw−ΔTsgsout+UsgAsgΔTsgΔ.


### 2.3. Coupling Process

In the NPP model,Δn,ΔP, ΔTcout,ΔTsgpin, and ΔTsgpout,ΔTcin are three pairs of couple variables:(10)ΔP=ΣfΔnUeΒ3.125×1010Δn,ΔTsgpin+τ1dΔTsgpindt=ΔTcout,ΔTcin+τ2dΔTcindt=ΔTsgpout,where τ1 is the time delay from reactor core outlet to UTSG inlet, and τ2 is the time delay from UTSG outlet to reactor inlet.If the control rod reactivity and feedwater temperature are regarded as system input, the coupling process of the NPPs can be shown as Figure3, and the NPP model can be converted to state space (11):(11)dxdt=Ax+Bu,where(12)x=ΔnΔC1⋯ΔC6ΔTfΔTcoutΔTcinΔTsgpinΔTsgpoutΔTsgsout,(13)A=δ0−βΛλ1⋯0⋯0β1Λ−λ10⋯0⋯0⋮β6Λ0⋯0−λ60⋯0∑fΔnUeB3.125×1010ρfVfCf0⋯0−UtAcρfVfCfUtAc2ρfVfCfUtAcρfVfCf0000⋯02UtAcρcVcCp−UtAc+2GpCp2ρcVcCp2GpCp−UtAc2ρcVcCp+1τ20−1τ200⋯000−1τ201τ200⋯001τ101τ1000⋯00−1τ102GpCp−UsgAsg2ρsgpVsgpCp+1τ1UsgAsg+2GpCp2ρsgpVsgpCpUsgAsgρsgpVsgpCp0⋯0000UsgAsg2ρsgpVsgpCsUsgAsg2ρsgpVsgpCs−UsgAsg+2GsCs2ρsgpVsgpCs,(14)B=n0Λ0…0T.Figure 3
Coupling process of the NPPs.


## 2.1. Neutron Kinetic

According to the lumped parameter method, the nonlinear core model is established via using the point kinetics equations with six groups of delayed neutrons and two reactivity feedback mechanisms [18]. The normalized point kinetics equations for the critical core without external source of neutrons can be expressed as(1)dntdt=δt−βΛ+∑i=16λicit+qt,dcitdt=βiΛnt−λicit,i=1,2,…,6.The reactivity feedbacks in this model are expressed as a function of the average temperatures of fuel and coolant. As a result, the total reactivity is the control rod reactivity combined with the feedbacks described as(2)δt=δrod+αfTf−Tf0+αcoolantTp−Tp0,where the subscript 0 refers to a reference condition, taken at the rated power, n means the neutron density, ρ means the reactivity, β means the neutron fraction, Λ means the neutron generation time, λi means the decay constant of ith group, ci means the delayed neutron precursor concentration of ith group, δrod means the reactivity of rod, αf means the reactivity feedback of fuel, αcoolant means the reactivity feedback of coolant in reactor core, Tf means the temperature of fuel, Tf means the temperature of fuel at the rated power, and Tp means the average temperature of pressurized water of reactor core.It is assumed that the neutron density in steady state isn0, delayed neutron precursor concentration of ith group in steady state is ci0, and then the neutron kinetic model can be linearized as follows:(3)dΔntdt=δ0−βΛΔnt+n0ΛΔδt+∑i=16λiΔcit,dΔcitdt=βiΛΔnt−λiΔcit,where Δ means the increment.


## 2.2. Thermal-Hydraulic

### 2.2.1. Core

The reactor core is assumed to be a lumped cylindrical area as a function of the power [19]. The fission energy is released in the fuel elements in the form of heat. This heat is then transferred to the upcoming pressurized water. This process is described as follows:(4)ρfVfCfdTfdt=P−UtAcTf−Tc,(5)ρcVcCpdTcdt=UtAcTf−Tc−GpCpTcout−Tcin,where ρf and ρc mean the fuel density and the primary coolant density in the reactor core, respectively, Vf means the fuel volume, P means the reactor power, Ut means the heat transfer coefficient between fuel and primary coolant, Ac means the fuel assemblies area, Cf and Cp the mean specific enthalpy of fuel and primary coolant, respectively, Tf and Tc mean fuel and primary coolant temperatures, respectively, and Gp means the mass flow rate of primary loop.Accordingly, the increment form of equations (4) and (5) can be given as(6)ρfVfCfdΔTfdt=ΔP−UtAcΔTf−ΔTc,ρcVcCpdΔTcdt=UtAcΔTf−ΔTc−GpCpΔTcout−ΔTcin.


### 2.2.2. Steam Generator

Usually, steam generators in NPPs will be of U-tubes and counter current type. Single-phase pressurized water and two-phase water are in shell-side and tube-side of USTGs, respectively. In order to give a simple description for the control-oriented modeling, one-section model is adopted to describe the main thermodynamics of UTSGs:(7)ρsgpVsgpCpdTsgpdt=GpCpTsgpin−Tsgpout−UsgAsgTsgΔ,(8)ρsgsVsgsdTsgsdt=GsCsTfw−Tsgsout+UsgAsgTsgΔ,where Tsgp means the average coolant temperature in the primary side of UTSGs, Tsgpin and Tsgpout mean inlet and outlet coolant temperatures in the primary side of UTSGs, TsgΔ means the temperature difference between the coolant flows in the two sides of UTSGs, which can be given by TsgΔ=Tsgp−Tsgs, where Tsgp and Tsgs mean average coolant temperatures in primary and secondary sides of UTSGs, respectively, Tfw means the feedwater temperature, Tsgsout means the outlet temperature in secondary side of UTSGs, Usg and Asg mean the heat transfer coefficient and area between the two sides of UTSGs, respectively, and Vsgp and Vsgs mean primary and secondary side volume of UTSGs, respectively.Accordingly, the increment form of equations (7) and (8) can be given as(9)ρsgpVsgpCpdΔTsgpdt=GpCpΔTsgpin−ΔTsgpout−UsgAsgΔTsgΔ,ρsgsVsgsCsdΔTsgsdt=GsCsΔTfw−ΔTsgsout+UsgAsgΔTsgΔ.


## 2.2.1. Core

The reactor core is assumed to be a lumped cylindrical area as a function of the power [19]. The fission energy is released in the fuel elements in the form of heat. This heat is then transferred to the upcoming pressurized water. This process is described as follows:(4)ρfVfCfdTfdt=P−UtAcTf−Tc,(5)ρcVcCpdTcdt=UtAcTf−Tc−GpCpTcout−Tcin,where ρf and ρc mean the fuel density and the primary coolant density in the reactor core, respectively, Vf means the fuel volume, P means the reactor power, Ut means the heat transfer coefficient between fuel and primary coolant, Ac means the fuel assemblies area, Cf and Cp the mean specific enthalpy of fuel and primary coolant, respectively, Tf and Tc mean fuel and primary coolant temperatures, respectively, and Gp means the mass flow rate of primary loop.Accordingly, the increment form of equations (4) and (5) can be given as(6)ρfVfCfdΔTfdt=ΔP−UtAcΔTf−ΔTc,ρcVcCpdΔTcdt=UtAcΔTf−ΔTc−GpCpΔTcout−ΔTcin.


## 2.2.2. Steam Generator

Usually, steam generators in NPPs will be of U-tubes and counter current type. Single-phase pressurized water and two-phase water are in shell-side and tube-side of USTGs, respectively. In order to give a simple description for the control-oriented modeling, one-section model is adopted to describe the main thermodynamics of UTSGs:(7)ρsgpVsgpCpdTsgpdt=GpCpTsgpin−Tsgpout−UsgAsgTsgΔ,(8)ρsgsVsgsdTsgsdt=GsCsTfw−Tsgsout+UsgAsgTsgΔ,where Tsgp means the average coolant temperature in the primary side of UTSGs, Tsgpin and Tsgpout mean inlet and outlet coolant temperatures in the primary side of UTSGs, TsgΔ means the temperature difference between the coolant flows in the two sides of UTSGs, which can be given by TsgΔ=Tsgp−Tsgs, where Tsgp and Tsgs mean average coolant temperatures in primary and secondary sides of UTSGs, respectively, Tfw means the feedwater temperature, Tsgsout means the outlet temperature in secondary side of UTSGs, Usg and Asg mean the heat transfer coefficient and area between the two sides of UTSGs, respectively, and Vsgp and Vsgs mean primary and secondary side volume of UTSGs, respectively.Accordingly, the increment form of equations (7) and (8) can be given as(9)ρsgpVsgpCpdΔTsgpdt=GpCpΔTsgpin−ΔTsgpout−UsgAsgΔTsgΔ,ρsgsVsgsCsdΔTsgsdt=GsCsΔTfw−ΔTsgsout+UsgAsgΔTsgΔ.


## 2.3. Coupling Process

In the NPP model,Δn,ΔP, ΔTcout,ΔTsgpin, and ΔTsgpout,ΔTcin are three pairs of couple variables:(10)ΔP=ΣfΔnUeΒ3.125×1010Δn,ΔTsgpin+τ1dΔTsgpindt=ΔTcout,ΔTcin+τ2dΔTcindt=ΔTsgpout,where τ1 is the time delay from reactor core outlet to UTSG inlet, and τ2 is the time delay from UTSG outlet to reactor inlet.If the control rod reactivity and feedwater temperature are regarded as system input, the coupling process of the NPPs can be shown as Figure3, and the NPP model can be converted to state space (11):(11)dxdt=Ax+Bu,where(12)x=ΔnΔC1⋯ΔC6ΔTfΔTcoutΔTcinΔTsgpinΔTsgpoutΔTsgsout,(13)A=δ0−βΛλ1⋯0⋯0β1Λ−λ10⋯0⋯0⋮β6Λ0⋯0−λ60⋯0∑fΔnUeB3.125×1010ρfVfCf0⋯0−UtAcρfVfCfUtAc2ρfVfCfUtAcρfVfCf0000⋯02UtAcρcVcCp−UtAc+2GpCp2ρcVcCp2GpCp−UtAc2ρcVcCp+1τ20−1τ200⋯000−1τ201τ200⋯001τ101τ1000⋯00−1τ102GpCp−UsgAsg2ρsgpVsgpCp+1τ1UsgAsg+2GpCp2ρsgpVsgpCpUsgAsgρsgpVsgpCp0⋯0000UsgAsg2ρsgpVsgpCsUsgAsg2ρsgpVsgpCs−UsgAsg+2GsCs2ρsgpVsgpCs,(14)B=n0Λ0…0T.Figure 3
Coupling process of the NPPs.


## 3. Analysis and Design of Control System

### 3.1. Formulation of Control Problem

Generally, the full state feedback can be used for the whole plant control system. However, in this work, it is assumed that the control system cannot depend on neutron flux feedback from neutron sensors in core or out of core, so that, as a part of state feedback, the nuclear core power should be reconstructed by the output state. As mentioned in Section1, the accuracy of temperature sensors in the secondary loop can be guaranteed, because maintenance and replacement of temperature sensors in the secondary loop are more convenient than the temperature sensors in primary loop. So, the outlet temperature increment is regarded as the output variable of system (11), as shown as the following equation:(15)y=Cx,where(16)C=ΣfΔnUeΒ3.125×10100⋯0.The control problem in this work can be given as follows:For system (11) and output (14), design a control system to make the state x converge to 0, where Δn or ΔP cannot be measured.


### 3.2. Observer Design

Accordingly, the observer of core power and core temperature can be given as follows:(17)x^=Oy.In fact, equation (17) is an open loop observer. There are two disadvantages for this observer:(1)
The initial statex0 is necessary(2)
Ifx^0 or x0 has deviation caused by system perturbation, the error e˜≜x−x^ will be unstable because the state matrix A has eigenvalues with a positive real partTo improve observation performance, the closed loop observer needs to be built. Accordingly, the closed loop observer model can be given as follows [20]:(18)x^˙=A−LCx^+Ly+Bu.The observation of equation (17) is asymptotically stable. x^ can be regarded as the estimate of x at any time. Actually, the key problem is the eigenvalues configuration of the matrix A−LC. The system ATCT is controllable if the system AC is observable. Further, it can be shown that eigenvalues of AT+CTK can be configured arbitrarily. If L=−KT, one has(19)A+KTC=A−LC,where K means the state feedback matrix.It is obvious that eigenvalues ofA−LC can also be configured arbitrarily.


### 3.3. Controller Design

The controller designed in this work needs to depend on the estimatex^. The system with asymptotical state observer (17) can be rewritten as follows:(20)x˙x^˙=ABKLCA+BK−LCxex^˙+BBv.Under the linear transformationx˙e˙=Tx˙x^˙, one has(21)x˙e˙=A+BK−BK0A−LCxe+B0v,(22)y=C0xe,where(23)T=In0In−In.It is obvious thatT cannot change feature frequencies, so that the feature spectrums of (20) and (21) can be given as(24)σA′=σA+BK⊕σA−LC,where(25)A′=ABKLCA+BK−LC.According to equation (24), system (21) consists of a closed loop subsystem with state feedback x and an estimate subsystem. If the system AC is observable, the feature spectrum σA−LC of the estimate subsystem can be configured arbitrarily by the matrix L; if the system AB is controllable, the feature spectrum σA+BK can also be configured arbitrarily by the matrix K.Because of the characteristic of separation design, the feedback matrix can be designed according to the algorithm of pole assignment:(1)
IfAcBcCc is the controllable form of system (11), calculate the characteristic polynomial Ps=∏i=113s−pi=s13+∑i=012αisi of AcBcCc, where pi means the ith pole(2)
If the idea poles arepi¯,i=1,…,13, calculate the polynomial Ps¯=∏i=113s−pi¯(3)
The feedback matrixK can be given as(26)K=α−α¯,where α=α0…α12, α¯=α0¯…α12¯, and(27)αi¯=1i!diPs¯dti|s=0.


## 3.1. Formulation of Control Problem

Generally, the full state feedback can be used for the whole plant control system. However, in this work, it is assumed that the control system cannot depend on neutron flux feedback from neutron sensors in core or out of core, so that, as a part of state feedback, the nuclear core power should be reconstructed by the output state. As mentioned in Section1, the accuracy of temperature sensors in the secondary loop can be guaranteed, because maintenance and replacement of temperature sensors in the secondary loop are more convenient than the temperature sensors in primary loop. So, the outlet temperature increment is regarded as the output variable of system (11), as shown as the following equation:(15)y=Cx,where(16)C=ΣfΔnUeΒ3.125×10100⋯0.The control problem in this work can be given as follows:For system (11) and output (14), design a control system to make the state x converge to 0, where Δn or ΔP cannot be measured.


## 3.2. Observer Design

Accordingly, the observer of core power and core temperature can be given as follows:(17)x^=Oy.In fact, equation (17) is an open loop observer. There are two disadvantages for this observer:(1)
The initial statex0 is necessary(2)
Ifx^0 or x0 has deviation caused by system perturbation, the error e˜≜x−x^ will be unstable because the state matrix A has eigenvalues with a positive real partTo improve observation performance, the closed loop observer needs to be built. Accordingly, the closed loop observer model can be given as follows [20]:(18)x^˙=A−LCx^+Ly+Bu.The observation of equation (17) is asymptotically stable. x^ can be regarded as the estimate of x at any time. Actually, the key problem is the eigenvalues configuration of the matrix A−LC. The system ATCT is controllable if the system AC is observable. Further, it can be shown that eigenvalues of AT+CTK can be configured arbitrarily. If L=−KT, one has(19)A+KTC=A−LC,where K means the state feedback matrix.It is obvious that eigenvalues ofA−LC can also be configured arbitrarily.


## 3.3. Controller Design

The controller designed in this work needs to depend on the estimatex^. The system with asymptotical state observer (17) can be rewritten as follows:(20)x˙x^˙=ABKLCA+BK−LCxex^˙+BBv.Under the linear transformationx˙e˙=Tx˙x^˙, one has(21)x˙e˙=A+BK−BK0A−LCxe+B0v,(22)y=C0xe,where(23)T=In0In−In.It is obvious thatT cannot change feature frequencies, so that the feature spectrums of (20) and (21) can be given as(24)σA′=σA+BK⊕σA−LC,where(25)A′=ABKLCA+BK−LC.According to equation (24), system (21) consists of a closed loop subsystem with state feedback x and an estimate subsystem. If the system AC is observable, the feature spectrum σA−LC of the estimate subsystem can be configured arbitrarily by the matrix L; if the system AB is controllable, the feature spectrum σA+BK can also be configured arbitrarily by the matrix K.Because of the characteristic of separation design, the feedback matrix can be designed according to the algorithm of pole assignment:(1)
IfAcBcCc is the controllable form of system (11), calculate the characteristic polynomial Ps=∏i=113s−pi=s13+∑i=012αisi of AcBcCc, where pi means the ith pole(2)
If the idea poles arepi¯,i=1,…,13, calculate the polynomial Ps¯=∏i=113s−pi¯(3)
The feedback matrixK can be given as(26)K=α−α¯,where α=α0…α12, α¯=α0¯…α12¯, and(27)αi¯=1i!diPs¯dti|s=0.


## 4. Results and Discussion

### 4.1. Reference Design

To verify the efficiency of the control strategy and the controller in Section3, the CPR1000 is regarded as the reference design.CPR1000 (Chinese pressurized reactor) is a three-loop 1000 MWe pressurized water reactor (PWR). It is an advanced, mature, safe, and economical nuclear reactor which is an updated version of Daya Bay Nuclear Reactor. The CPR1000 utilizes the proven technology, which builds on nearly 40 years of operating PWR experience. The major parameters of CPR1000 are listed in Table1 [21].Table 1
Major parameters of CPR1000.
ParametersValueReactor typePWRFuel typeUO2Core power2895MW (thermal)Steam generatorU-tube natural circulationPrimary pumpNonseal centrifugal pumpOperating pressure15.5MPaCore inlet temperature292.4°CCore outlet temperature327.6°CDesign volume flow flux22840m3/hMeanwhile, the simulator with CPR1000 type is used for accurate dynamic simulation. The structure of CPR1000 simulation model is shown schematically in Figure4. For ease of the verification, three components of the model structure are extracted: the reactor core, primary loop, and USTG. The steam turbine, condenser, third loop, and other auxiliary components are instead of temperature and pressure boundaries.Figure 4
CPR1000 simulation model.


### 4.2. Poles Distribution

According to the control strategy in Section3.1, the closed loop poles without the controller in Section 3.2 can be given as Figure 5. It is obvious that the system is not stable, because there are a pair of complex poles in the right half of the plane 20.8±25.5i, so that we should reconfigure the unstable poles according to the method in Section 3.2. The pair of complex poles is reset at 0.22±0.47i, which can be shown in Figure 6. Meanwhile, three pairs of complex poles, 0.22±0.47i, 0.324±0.00836i, and 0.361±0.101i, become the predominant poles. Accordingly, the feedback matrix can be given according to equation (26). Furthermore, the observer of core power can also be designed according to equation (18).Figure 5
Closed loop pole distribution without the controller in Section3.3.Figure 6
Closed loop pole distribution with the controller in Section3.3.


### 4.3. Dynamic Response

For verifying the effectiveness clearly, two dynamic responses are calculated: one is the response of the linear model equation (11), and the other is the response of the model in the CPR1000 simulator.In the initial condition, the core power is at 80% FP, and the mass flow of primary loop is kept constant. At the 1st sec, the setting power is changed from 80% FP to 100% FP. It is assumed that the out-of-core neutron sensors fail completely. The neutron flux feedback can be given by the observer equation (18), where the input contains core outlet coolant temperature and UTSG outlet coolant temperature in secondary side. The dynamic response of core power, core outlet temperature increment, and UTSG outlet temperature increment can be shown as Figures 7–9. Before 100th sec, the core power and temperature increment dynamic response of system equation (11) have an overshoot of less than 10% and 5%, respectively. After 400th sec, the core power and temperature increment tend towards stability. In comparison, the power and temperature increment dynamic responses have same steady state although that they have longer response time. This is due to that some high-frequency components in the simulator are neglected in the linear model equation (11).Figure 7
Power level response of linear model equation (11) and CPR1000 simulator.Figure 8
Core outlet temperature response of linear model equation (11) and CPR1000 simulator.Figure 9
UTSG outlet temperature response of linear model equation (11) and Yangjiang NPP simulator.


## 4.1. Reference Design

To verify the efficiency of the control strategy and the controller in Section3, the CPR1000 is regarded as the reference design.CPR1000 (Chinese pressurized reactor) is a three-loop 1000 MWe pressurized water reactor (PWR). It is an advanced, mature, safe, and economical nuclear reactor which is an updated version of Daya Bay Nuclear Reactor. The CPR1000 utilizes the proven technology, which builds on nearly 40 years of operating PWR experience. The major parameters of CPR1000 are listed in Table1 [21].Table 1
Major parameters of CPR1000.
ParametersValueReactor typePWRFuel typeUO2Core power2895MW (thermal)Steam generatorU-tube natural circulationPrimary pumpNonseal centrifugal pumpOperating pressure15.5MPaCore inlet temperature292.4°CCore outlet temperature327.6°CDesign volume flow flux22840m3/hMeanwhile, the simulator with CPR1000 type is used for accurate dynamic simulation. The structure of CPR1000 simulation model is shown schematically in Figure4. For ease of the verification, three components of the model structure are extracted: the reactor core, primary loop, and USTG. The steam turbine, condenser, third loop, and other auxiliary components are instead of temperature and pressure boundaries.Figure 4
CPR1000 simulation model.


## 4.2. Poles Distribution

According to the control strategy in Section3.1, the closed loop poles without the controller in Section 3.2 can be given as Figure 5. It is obvious that the system is not stable, because there are a pair of complex poles in the right half of the plane 20.8±25.5i, so that we should reconfigure the unstable poles according to the method in Section 3.2. The pair of complex poles is reset at 0.22±0.47i, which can be shown in Figure 6. Meanwhile, three pairs of complex poles, 0.22±0.47i, 0.324±0.00836i, and 0.361±0.101i, become the predominant poles. Accordingly, the feedback matrix can be given according to equation (26). Furthermore, the observer of core power can also be designed according to equation (18).Figure 5
Closed loop pole distribution without the controller in Section3.3.Figure 6
Closed loop pole distribution with the controller in Section3.3.


## 4.3. Dynamic Response

For verifying the effectiveness clearly, two dynamic responses are calculated: one is the response of the linear model equation (11), and the other is the response of the model in the CPR1000 simulator.In the initial condition, the core power is at 80% FP, and the mass flow of primary loop is kept constant. At the 1st sec, the setting power is changed from 80% FP to 100% FP. It is assumed that the out-of-core neutron sensors fail completely. The neutron flux feedback can be given by the observer equation (18), where the input contains core outlet coolant temperature and UTSG outlet coolant temperature in secondary side. The dynamic response of core power, core outlet temperature increment, and UTSG outlet temperature increment can be shown as Figures 7–9. Before 100th sec, the core power and temperature increment dynamic response of system equation (11) have an overshoot of less than 10% and 5%, respectively. After 400th sec, the core power and temperature increment tend towards stability. In comparison, the power and temperature increment dynamic responses have same steady state although that they have longer response time. This is due to that some high-frequency components in the simulator are neglected in the linear model equation (11).Figure 7
Power level response of linear model equation (11) and CPR1000 simulator.Figure 8
Core outlet temperature response of linear model equation (11) and CPR1000 simulator.Figure 9
UTSG outlet temperature response of linear model equation (11) and Yangjiang NPP simulator.


## 5. Conclusion

In this work, a power control system of NPPs based on power observer is developed. When the out-of-core neutron sensors fail, the traditional power level control system cannot work because accurate neutron flux and total power in the reactor core cannot be provided. However, because of the separation principle, the neutron flux or total power in the reactor core can be observed by the coolant temperature in the secondary loop and independent from power controller design, so that the state observer and controller are designed, respectively, and the effectiveness of the power level controller based on the state observer is verified by the NPP simulator. The analysis shows consistency of results between the linear model and NPP simulator, which indicates that the power level controller based on the state observer is effective, although there is difference in the dynamic response, which is caused by the truncation of the high frequencies.In the future work, we will focus on the nonlinear core power observer and eliminate the dynamic deviation caused by the truncation for high frequencies.



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*Source: 8833729-2021-02-03.xml*