【正文】 in the outofplane direction and thus avoids enormously high nonphysical outofplane stresses. The 8noded generalized plane strain elements CPEG8 have been used here. B. Thermal Simulation During the operating mode, it should be accounted for a heat flux of 250 up to 500 kW/m2 (peak) on the plasmafacing side as well as a heat flux of 60 kW/m2 and of 35 kW/m2 on the vertical and horizontal interior, respectively, due to breeder units, see fig. 2. For the reason of simplicity, boundary conditions depicted in fig. 2 have been considered in the simulations. C. Mechanical Simulations using various Plasma Heating and Pressure in Cooling Channels (no cycling) By variation of both the temperature in cooling channels and the plasma heating, a critical pressure has been determined. The critical pressure is defined as the minimum pressure causing an inelastic deformation after the 1st heating . After the 1/2 of the 1st cycle. The critical pressure is shown in fig. 3 in dependence on the plasma heating and the temperature in the cooling channels Tcc. Evidently, the critical pressure is strongly dependent on the temperature in the cooling channels and relatively slightly on the plasma heating up to 450 500 kW/m2 approximately. Increasing plasma heating takes however a leading influence on the critical pressure whereas the temperature in the cooling channels plays a decreasing role and, finally, plastic deformation occurs for all Tec without pressure due to the temperature gradient alone if the plasma heating reaches 1000kW/M2. For this heating, the plastic deformation is localized in a narrow band along the plasmafacing side, see fig. 4 (on the left). A high pressure causes an additional plastic deformation located in a left bottom or left top corners of the 1St or 2nd cooling channels if the pressure in the channels reaches a critical value discussed above, see fig. 4 (on the right). The magnitude of the deformation is higher than the magnitude of the thermal plastic strain. 三。唯一的外部機(jī)械負(fù)載的非事故工作模式的 80欄 = 8兆帕斯卡的冷卻管道水壓。 2。臨界壓力被定義為最小壓力造成的經(jīng)過后， 1 /第 1周期 2第一加熱即一個(gè)彈性變形。等離子體加熱時(shí)間增加但就，而在冷卻通 道的溫度，臨界壓力的影響起著主導(dǎo)作用，減少由于沒有壓力，溫度梯度，如果僅達(dá)到 1000kW/M2等離子體加熱，最后，塑性變形對(duì)所有過渡時(shí)期發(fā)生。 4（右側(cè)）。 (2) a holding at the high temperature (HT) 400 sec, (3) a cooling to the RT, 100 sec and, finally (4) a holding at the RT 1400 sec. Note that the steps (2) and (4) are not relevant for the ABAQUSown timeindependent material model. It was possible to simulate 300 cycles with the ABAQUSown model and only 100 cycles with the UMAT because of the high cpu time needed. The results have been generated in a table format along the path AB,CD,GF and KL depicted in fig. 1. A followup examination has shown that the highest plastic strain in the model occurs near the point L of the path KL as in fig. 4 (on the right). A change of the maximum equivalent plastic strain near the point L within the first 100 cycles is depicted in fig. 5 for both material models used. A detailed investigation shows an almost linear increase of the equivalent plastic strain in the case of the ABAQUSown material model. However, the increase lies between and for the first 300 cycle. The application of the UMAT leads evidently to considerably higher plastic strains due to the creep and damage of the material. Note that the values of the variable PEMAG (the magnitude of the plastic strain) after the It heating are quite similar for both models, see fig. 5. The behavior of the maximum von Mises stress along the path KL for the first 10 cycles is illustrated in fig. 6 for both material models. For the same reason, the von Mises stress obtained using the UMAT is considerably less than in the case if the ABAQUSown model is applied. Note that the values of the von Mises stress are quite identical for both models after the Ist heating, see also fig. 6. The ABAQUSown model also leads to a material softening, wh