# Development and Application of the Power Plant Real-Time Temperature and Stress Monitoring System

Authors: Piotr Duda
Journal: Science and Technology of Nuclear Installations
 (2017)

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## Abstract

The paper presents a method of temperature and stress estimation in pressure components of conventional or nuclear power plants. The proposed algorithm can be applied without the information concerning the thermal boundary condition on the component inner surfaces and it is fast enough to be applied in an online mode. The solution is possible thanks to “measured” temperature histories determined in easily accessible points located on the component outer surface. The presented model has been recently verified analytically, numerically, and experimentally. The proposed algorithm was used to calculate the transient temperature and stress distribution in the outlet header of a steam reheater and the results indicate that the component lower part is loaded the most, but allowable stresses are not exceeded. If the presented heating process was shortened, the calculated stresses would exceed the allowable values. Monitoring the boiler thermal and strength operating conditions makes it possible to identify dangerous loads of the power boiler pressure elements during transient-state operations. The presented method for controlling thermal and pressure-related stresses is suitable for nuclear power plants because it does not require drilling holes for sensors in the pressure element walls.


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## Body

## 1. Introduction

The behaviour of components of conventional or nuclear power plants has been investigated in numerous research projects [1]. During their operation, high stresses occur in thick-walled pressure elements. The operation cyclic character resulting from the cooling and heating of pressure elements causes the low-cycle fatigue phenomenon, which may lead to cracks. As power plants become older engineers need screening criteria to eliminate the risk of thermal fatigue. A number of programs have been launched to develop fatigue monitoring systems for the nuclear power plant components [2, 3]. The use of monitoring systems has a significant impact on the remnant life prediction, highlighting hot zones in the boiler and the influence of modified operations on safe extension of the plant life [4]. The control system quality depends on the accuracy of stress calculations in selected elements of the power unit. The offline method of thermal stress evaluation by using the fluid-structure interaction in the piping system T-connections is presented in [5]. The whole area where the fluid is contained has to be discretized. Then the mass, momentum, and energy balance equations have to be written. Depending on the flow nature, it may also be necessary to introduce a suitable turbulence model. The calculations are more difficult in the case of two-phase flows that involve boiling or condensation processes. Green’s function method with consideration of temperature-dependent material properties is shown in [6]. The main disadvantage of this method is the need to find the heat transfer coefficient. Another way to determine the distribution of temperatures and stresses is to solve the inverse heat conduction problem in the device under analysis. Inverse methods enable determination of the entire time- and space-dependent temperature distribution in an element based on measured temperature histories in selected spatial points [7, 8]. The temperature distribution reconstructed in this manner makes it possible to calculate stresses in the analysed elements as accurately as possible [9].The aim of this work is to present an online temperature and stress monitoring method. The commercial computational software, which is available on the market today, does not make it possible to solve the problem under consideration in an online mode because thermal boundary conditions are not defined on the monitored component inner surfaces. The proposed method has already been tested on a laboratory stand [9]. This paper presents the application of the proposed algorithm for the calculation of the transient-state temperature and stress distribution in the outlet header of a power plant steam reheater. The presented method for controlling thermal and pressure-related stresses is suitable for nuclear power plants because it does not require drilling holes for sensors in the pressure element walls.


## 2. Formulation of the Method

The equation governing the transient-state heat conduction problem has the following form:(1)cTρT∂T∂t=-∇·q,where q is the heat flux vector. Fourier’s law for an isotropic material takes the following form:(2)q=-k∇T.All material properties (c: specific heat, ρ: density, and k: thermal conductivity) are assumed as known functions of temperature. The control volume finite element method is used [10]. Equation (1) is integrated over general control volume V with bounding surface S:(3)∫VcTρT∂T∂tdV=-∫V∇·qdV.By applying the mean value theorem for integrals on the left and the divergence theorem on the right, the following equation is obtained:(4)VcT-ρT-dT-dt=-∮Sq·ndS,where the bar indicates an average value in volume V andn is a normal unit surface vector directed to the outside of the control volume.If temperature does not vary in a cylindrical component along the generatrix but changes along the circumference and on the wall thickness, the unsteady-state temperature distribution is two-dimensionalT(r,ϕ,t).For such a problem, the analysis can be carried out only for a cross-section as presented in Figure1. The cross-section is divided into control volumes. Assuming that the component outer surface is perfectly insulated and an unknown boundary condition occurs on the inner surface, the inverse problem may be solved starting with a heat balance equation for the control volume associated with node i=40.Figure 1
Division of a cylindrical component cross-section into control volumes.The heat balance equation (4) for node i=40 has the following form: (5)dTidt=4air72-r62·Δφki+1+ki2ki·0.5·Δrr7·ΔφTi+1-Ti+ki-13+ki2ki·r6·0.5·ΔφΔrTi-13-Ti,where i=40, ki=kTi,ci=cTi,ai=ki/ci·ρi.Heat balance equations for control volumesi = 41–51 are expressed as follows:(6)dTidt=2air72-r62·Δφki-1+ki2ki·0.5·Δrr7·ΔφTi-1-Ti+ki-13+ki2ki·r6·ΔφΔrTi-13-Ti+ki+1+ki2ki·0.5·Δrr7·ΔφTi+1-Tiand for volume i=52 the following can be written:(7)dTidt=4air72-r62·Δφki-1+ki2ki·0.5·Δrr7·ΔφTi-1-Ti+ki-13+ki2ki·r6·0.5·ΔφΔrTi-13-Ti.Temperature histories in nodes 27–39 can be obtained from 13 equations (5)–(7) based on the T40–T52 measured data.If the material propertiesc,ρ, and k are temperature-dependent, the system of (5)–(7) can be solved iteratively. At first, temperature unknowns are assumed as(8)Tk0=T13+kk=27⋯39and after the first iteration they take the values of Tk1,k=27⋯39. The iterative algorithm continues until the following condition is satisfied:(9)Tkn+1-TknTkn+1≤ε,n=0,1,2,…,k=27⋯39.Each of the calculated temperature histories can also be determined independently.Once the temperature values in nodes 27 to 39 are obtained, an inverse solution can be run again to find the temperatures in points 14 to 26 by writing the heat balance equations for the control volumes associated with nodes 27 to 39:(10)dTidt=4air62-r42·Δφki+1+ki2ki·Δrr5·ΔφTi+1-Ti+ki-13+ki2ki·r4·0.5·ΔφΔrTi-13-Ti+ki+13+ki2ki·r6·0.5·ΔφΔrTi+13-Tifori=27,dTidt=2air62-r42·Δφki-1+ki2ki·Δrr5·ΔφTi-1-Ti+ki-13+ki2ki·r4·ΔφΔrTi-13-Ti+ki+1+ki2ki·Δrr5·ΔφTi+1-Ti+ki+13+ki2ki·r6·ΔφΔrTi+13-Tifori=28⋯38,dTidt=4air62-r42·Δφki-1+ki2ki·Δrr5·ΔφTi-1-Ti+ki-13+ki2ki·r4·0.5·ΔφΔrTi-13-Ti+ki+13+ki2ki·r6·0.5·ΔφΔrTi+13-Tifori=39.A similar system of equations can be written for volumes 14 to 26 to calculate temperature histories from nodes 1 to 13. Next, the temperature distribution in every time step is used to conduct a structural analysis. The aim of the monitoring algorithm is to reduce the highest stresses to allowable values. This restriction can be captured by a simple structural analysis based on elementary equations of thermoelasticity (the force equilibrium equation, the geometric equation, and the constitutive equation):(11)σij,j+fi=0,εij=12ui,j+uj,i,σij=2Gεij+λεkkδij-βTδij,where σ is a stress tensor, f is the body forces vector, u is a displacement vector, ε is a strain tensor, G andλ are Lame constants, β is a thermal expansion coefficient, and δij is the Kronecker delta [11].There are two types of boundary conditions defined by displacement or force. The finite element method is used to discretize the above equations. The structural numerical model is presented in Figure2. All inner surfaces of the header are loaded with internal pressure. One lateral surface of the chamber is loaded with longitudinal tension and the opposite lateral surface of the model is blocked at one point in the direction of the pipe axis. Additionally, the model is constrained to ensure symmetry conditions and is supported in two points in the direction of the vertical axis. Next, the calculated temperature distribution in every time step and in 52 points (see Figure 1) is approximated to 175 points on the cross-section of the model for the stress calculation (see Figure 2). Additionally, it is assumed that the same temperature distribution occurs in all other cross-sections of the model presented in Figure 2.Figure 2
Structural model division into finite elements and assumed boundary conditions.Solving inverse problems is more difficult compared to direct ones because inverse problems are ill-posed. The frequently observed oscillations in the solved transients can sometimes make the calculations completely unstable. There are many methods to solve this problem. One of them is to use smoothing filters to reduce the oscillations. The filters are based on local polynomial approximation (3rd-order kind and eleven subsequent measurement points) [7] and they smooth out the measured temperature curves.


## 3. Temperature and Stress Monitoring in a Power Plant

The presented method is used for temperature and stress monitoring in the outlet header of a steam reheater. The reheater is a component of a steam power boiler with the output of650·103 kg/h of steam characterized by the following parameters: p=13.5 MPa, T=540°C. The reheater outlet header is designed for the working pressure of pw=2.2 MPa and the steam working temperature of Tw=540°C. It is made of 15H1MF steel.Figure3 presents an example steam reheater outlet header which is used to collect or distribute generated steam. The part of the header without nozzles can be analysed by the model presented in Figure 2. Two horizontal nozzles can be seen in Figure 3. The component is also equipped with vertical nozzles.Figure 3
The steam reheater outlet header and the control panel with the data acquisition system.The dimensions of the component are as follows: outer diameterdo=630 mm, wall thicknesss = 30 mm, nozzle outer diameter don=44.5 mm, and nozzle wall thickness sn=4.5 mm. Allowable stresses σmin=-234.6MPa and σmax=295.3 MPa are determined using a fatigue strength diagram [12] under the assumption that the number of start-ups from a cold state is n=2000.The temperature and stress distributions in the reheater outlet header are obtained based on temperature transients, which are measured in seven points on the outer insulated surface [13]. It is assumed that a cylindrical element can expand and bend freely.Figure4 presents the steam pressure and temperature transients measured in seven points on the header thermally insulated outer surface. The measured temperature transients are approximated to 13 points on the outer surface. Based on (5)–(10), the inverse method calculates the temperature transients in 52 points on the header cross-section presented in Figure 1. An in-house program was developed and applied in the data acquisition system presented in Figure 3. The temperature distribution is calculated by means of the control-volume finite element method and the stress distribution by means of the finite element method.Figure 4
Measured steam pressure and temperature transients on the reheater outer header surface; nodes 44–52 are shown in Figure1.The temperature transients calculated in seven points on the header inner surface are presented in Figure5. After 500 s of the heating operation the temperature in point 1 drops to 148°C, which is close to saturation temperature at the measured steam pressure of 0.32 MPa. At that instant, the temperature of the upper part of the steam header (points 7, 9, 11, and 13) is considerably higher and the temperature difference between the lowest and the highest point on the inner surface equals 67°C. This is most probably the effect of the flow of nonevaporated water from the reheater nondrained coil pipes to the reheater outlet header. The temperature differences recorded on the header circumference create thermal stresses, which are presented in Figures 6 and 7. As the reheated steam pressure is relatively low, the pressure-related stresses in the header are small. The highest absolute circumferential and longitudinal stresses are tensile and they occur in the header lower, colder part. They reach their highest value after 450 s of the heating period and total 53.6 MPa and 75.7 MPa, respectively. These values are about 30% lower than those presented in [13], which is due to the presented numerical model better accuracy compared to the method used in [13]. The number of finite volumes in the inverse solution is increased from 28 to 52. The plane structural model with 52 nodes is upgraded to a 3D structural model with six elements on the wall thickness, 24 along the circumference and 34 along the horizontal axis. The longitudinal thermal stress distribution on the outlet header cross-section after 450 s of the heating operation is presented in Figure 8. The highest compressive circumferential and longitudinal stresses arise after 690 s of the heating period, totalling −31.8 MPa and −40.2 MPa, respectively.Figure 5
Temperature transients on the outlet header inner surface and the temperature difference transient between the outlet header top and bottomΔT=T13-T1.Figure 6
Circumferential thermal stress transients in seven points on the outlet header inner surface.Figure 7
Longitudinal thermal stress transients in seven points on the outlet header inner surface.Figure 8
Longitudinal thermal stress distribution in the outlet header cross-section after 450 s [MPa].In order to estimate stresses arising on the downcomer hole edges, thermal stresses are calculated in a cylindrical component and in a cylindrical component weakened by a nozzle. Since the geometry of the header with one nozzle is symmetrical, 1/4 of the construction element is modelled and analysed. The numerical model of a cylindrical element with a nozzle is presented in Figure10. It is assumed that the outer surface of the two components with a uniform initial temperature T0=20°C is ideally insulated and that the components are heated by steam on their inner surface. The steam temperature rises at a constant rate of vt=46.9 K/min.Next, the model is constrained to ensure symmetry conditions and to allow for the possibility of free lengthening in the direction of the header and the nozzle axis. The temperature distribution in every time step is used for a structural analysis. The maximum compressive circumferential thermal stresses in a cylindrical component with and without a nozzle are presented in Figure9. The thermal stress concentration factor αt=2.05 is calculated after 800 s of the heating process, when a quasi-steady-state occurs. The minimum and the maximum stress on the downcomer hole edges can be estimated at −82.4 MPa and 155.2 MPa, respectively. The values do not exceed the allowable stresses σmin=-234.6MPa and σmax=295.3MPa.Figure 9
Maximum compressive circumferential thermal stress in a cylindrical component with and without a nozzle.Figure 10
Division of the model of a cylindrical element with a nozzle into finite elements and the assumed boundary conditions.If the presented heating process was shortened from 1500 s to 600 s, the recorded stresses would be much higher. Figure11 presents the longitudinal thermal stress transients in seven points on the outlet header inner surface when the heating operation is faster. The minimum and the maximum stress on the downcomer hole edges can be estimated at −113.5 MPa and 304.9 MPa, respectively. The maximum tensile thermal stress exceeds the allowable value.Figure 11
Longitudinal thermal stress transients in seven points on the outlet header inner surface during the faster heating process.


## 4. Conclusions

The paper presents a method of temperature and stress estimation in pressure components of conventional or nuclear power plants. The proposed algorithm can be applied without the information concerning the thermal boundary condition on the component inner surfaces and it is fast enough to be applied in an online mode. The solution is possible thanks to “measured” temperature transients determined in easily accessible points located on the component outer surface. An application of the proposed algorithm for the calculation of the transient temperature and stress distribution in the steam reheater outlet header indicates that the component lower part is loaded the most. This is probably the effect of the flow of nonevaporated water, which did not leave the reheater through the coil draining pipes. The highest absolute stress is the tensile longitudinal stress. In order to estimate stresses on the hole edges, the thermal stress concentration factor is calculated. The minimum and the maximum stresses on the downcomer hole edges do not exceed the allowable values. Additionally, a modification of the presented process is assumed. If the heating process was shortened from 1500 s to 600 s, the recorded tensile stress on the downcomer hole edges would exceed the allowable value.Monitoring the boiler thermal and strength operating conditions makes it possible to identify dangerous loads of the power boiler pressure elements during transient-state operations. All the histories of stresses arising due to pressure and thermal loads are the basis for determining the creep and fatigue wear factors for pressure components. The presented method for controlling thermal and pressure-related stresses is suitable for nuclear power plants because it does not require drilling holes for sensors in the pressure element walls.



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*Source: 1812835-2017-11-20.xml*