WO1993001319A1

WO1993001319A1 - Material and workpiece for nuclear engineering and production thereof

Info

Publication number: WO1993001319A1
Application number: PCT/DE1991/000566
Authority: WO
Inventors: Dietrich Alter; Peter Dewes; Friedrich Garzarolli; Roland Hahn
Original assignee: Siemens Aktiengesellschaft
Priority date: 1991-07-10
Filing date: 1991-07-10
Publication date: 1993-01-21
Also published as: JPH06508885A; EP0593470A1

Abstract

Austenitic steel for nuclear reactor components is largely resistant to radiation-induced stress cracking corrosion if the silicon, phosphorus and sulphur content is reduced by comparison with commercial grades of steel and its grain structure has finely dispersed and distributed carbide deposits, especially niobium carbide. The finely dispersed distribution can be obtained if larger niobium deposits are first disagregated by annealing at 1100 to 1150 °C and the carbide is deposited by subsequent annealing at temperatures of about 750 °C.

Description

Material and workpiece for the core technology as well as the corresponding production

The invention relates to an austenitic steel for use in the radiation zone of a nuclear reactor and a workpiece made of this austenitic steel. The invention further relates to the production of this steel or workpiece.

The starting point is austenitic steel grades, the alloy components of which are largely standardized, e.g. steel with the German material number 1.4550, for which a carbon content of less than 0.1% by weight, a niobium content above eight times the carbon content, a chromium content of 17 to 19% by weight and a nickel content of 9 to 11.5 % By weight are prescribed. For other impurities, Mn 2.0, Si 1.0, P 0.045, S 0.03% by weight are given.

The properties of the base metal iron are modified by the prescribed amounts of the alloyed constituents and the upper limits of certain impurities with regard to the requirements of certain areas of application, the maximum limits of the impurities generally being chosen so that the alloy is made from standardized, cheap starting materials of commercial purity, Eg certain types of scrap can be produced efficiently. The upper limits of many impurities result from optimization of the manufacturing process, while the concentrations of other alloy components are determined by optimization of the material properties. For example, steel grades 1.4301 and 1.4401 only contain niobium as an impurity, but are practically the same as steel 1.4550 in terms of other impurities. In the United States, roughly equivalent steel grades are AISI 348, 304 and 316. The structure of such a material depends both on its components and on the temperature treatment and other process steps in its manufacture. For example, if the material is exposed to high temperatures for a long time, large grains form. Impurities and / or the use of lower temperatures during production inhibit grain growth. Coarse deformations, such as extrusion, rolling or forging with high forces, deform the grains, whereby large grains, which may be formed when the melt solidifies, can also be broken up by recrystallization. The grain structure in the finished material can influence certain material properties, such as strength or ductility. A high ductility may be required if the material is subjected to high stresses in a point-like manner, which must be absorbed and compensated for by the material. High thermal conductivity, mechanical stability and elasticity or corrosion resistance are also often required.

Austenitic steels are distinguished from other steels by their favorable mechanical properties and, at the same time, high resistance to uniform corrosion, as occurs under normal corrosive conditions. This corrosion removes the surface of the workpiece evenly. They were therefore used early on as a material for highly stressed structural parts inside a nuclear reactor. Operating experience and special tests show that these materials fail even at low elongations, which is attributed to selective corrosion at the grain boundaries ("intergranular corrosion", IK). This selective attack on the grain boundaries can occur outside of the reactor

Laboratory tests ("outpile test") are examined by corrosion tests under special, aggressive conditions. This shows, however, that austenitic steels that are resistant to IK without the influence of radiation, nevertheless still under the beam Oil exposure in the reactor fails. This typical reactor

Failure mechanism is therefore called "radiation-assisted stress crack corrosion (IASCC)". It is assumed that phosphorus and silicon are excreted at the grain boundaries and there lead to local embrittlement and susceptibility to corrosion. Based on Outpile-IK tests, the article "Behavior of Water Reactor Core Materials with Respect to Corrosion Attack" by Garzarolli, Rubel and Steinberg, "Proceedings of the International Symposium on Environmental Degradation of Materials in Nuclear Power Systems - Water Reactors ", Myrtle Beach, South Carolina, August 22-25, 1983, pages 1 through 23 recommended to keep the silicon content below 0.1% by weight and the phosphorus content below 0.01% by weight, but at the same time pointed out that radiation in the reactor increases the susceptibility to selective corrosion.

In "Deformability of Austenitic Stainless Steel and Ni-Base Alloys in the Core of a Boiling and a Pressurized Water Reactor" Proceedings of the 2nd International Symposium on Environmental

Degradation of Materials in Nuclear Power Systems - Water Reacto Monterey / California, September 9-12, 1985, pages 131 to 138, Garzarolli, Alter and Dewes report on outpile and inpile IK experiments on the influence of contaminants by phosphorus, Silicon and sulfur. Commercially available steel grades of material numbers 1.4541 and AISI 316 and 348, which were subjected to annealing at 1050 "C and a cold deformation of about 10% after the rough deformation, were analyzed with regard to their alloy constituents. A steel AISI 348 was compared with a sample, the content of which Silicon and phosphorus (0.59% by weight and 0.017% by weight) were reduced to 0.01% by weight and 0.008% by weight by means of a special cleaning process. The sulfur content was not analyzed The composition of this high-purity steel was 0.041% by weight of C, 11.1% by weight of Ni, 17.7% by weight of Ch, 1.65% by weight of Mn, 0.76% by weight of Nb + Ta. The temperatures for the rough deformation subsequent anneals were not strictly controlled and were in any case not above 1040 ° C., with a grain size of ASTM number 9 being obtained. The high-purity sample already showed one in the outpile test

significantly reduced rate of corrosion, and in-pipe tests with corresponding cladding tubes filled with ceramic swelling under radiation showed that the high-purity material alone survived a relative diameter change of 0.7% and even 1.4% without damage after irradiation.

Subsequently, however, tests with newly manufactured pipes showed that this positive result was accidental and not reproducible. Rather, the radiation-induced stress corrosion cracking (IASCC) is obviously responsible for factors and parameters that were obtained by chance during the aforementioned successful experiment and were not recorded or checked. For example, known from studies on zirconium alloys for nuclear technology that nitrogen leads to embrittlement and increased corrosion. Therefore was also at

austenitic steel suspected a significant influence of the nitrogen content and proposed an austenitic steel with 0.025% to 0.067% carbon and 1.5 to 2% by weight manganese, which has a maximum content of 0.03% by weight N, 0.005% by weight 56 P,

0.05 wt% Si and 0.005 wt% S (U.S. Patent 4,836,976).

Long-term tests in the reactor, however, showed that with these and similar materials with high purity in terms of P, S, N and Si, the ductility and resistance to IASCC of the singular test mentioned could not be achieved again. Also

With a systematic variation of the N content, no significant influence of this contamination could be demonstrated. All highly pure variants failed in inpile tests, so that the previously found high resistance to the one mentioned was unique

produced material is to be regarded as a random success, the Cause in random, unavoidable variations of the

Composition and / or the manufacturing process.

Since the exact processes involved in this IASCC behavior and suitable measures to avoid them are largely unknown, and because the number of possible influences is very large and the corresponding test series are always longer

Require use in the reactor, are extremely lengthy and complex, it is a previously unsolved task, e.g. Produce cladding tubes for absorber elements or other structural parts in the radiation zone of a nuclear reactor and a material suitable for this from an austenitic steel, the against

radiation-induced stress corrosion cracking sufficient

are resistant and to the stresses of a

Reactor operation can be suspended.

The present invention serves to achieve this object.

Ultimately, the aim is to reliably reproduce a one-off and randomly produced material with favorable mechanical and corrosive properties with regard to the parameters important for these properties. But it is already impossible with a reasonable effort

Known parameters of this material (austenitic steel with the following components: 11.1% Ni, 17.7% Cr, 1.65% Mn, 0.76% Nb + Ta, 0.01% Si, 0.08% P) by thermal treatment of a roughly deformed blank with temperatures up to 1040 "C, and with an ASTM number 9 for the particle size). In addition, it is unknown whether other, not recorded in the known material

Parameters are responsible for the observed positive results. According to the invention, certain parameters which are sufficient for these positive results and which can include partly previously recorded and partly undetected material parameters are selected, checked and set.

A controlled setting is not for other parameters required; they can arise, for example, from the requirements of further mechanical processing or also accidentally. The material or the corresponding workpiece produced according to the invention differs from that

Unique and randomly produced material due to reproducible resistance to IASCC.

The invention is based on the assumption that contamination by phosphorus, sulfur and silicon in particular promote radiation-induced stress corrosion cracking if they are present as segregation in the grain sizes of the material. The content of these impurities can be compared to conventional ones

Steel qualities can be reduced by appropriate cleaning measures, but practically complete purity is not possible. On the other hand, the average grain diameter of such a material increases the lower the concentration of these impurities; this reduces the number of grains and the total sum of the grain interfaces, so that despite the increased purity there are inadmissibly high accumulations of these impurities at the reduced interfaces

can come.

The invention therefore also assumes that larger, disruptive segregations of these contaminants can be avoided if there are sufficient collection points in the material at which these contaminants are collected. Suitable collection points in the material are finely dispersed carbides.

The invention therefore provides an austenitic steel for workpieces in the radiation area of nuclear reactors which, compared to commercial steel grades with their technical purity and their structure, has a reduced content of contaminating silicon, phosphorus and sulfur as well as a structure with fine grains, in which one contained in the steel Carbon practically completely as a carbide formed from an alloy additive in a controlled by ther mix treatment of steel adjustable fine disperse

Distribution is eliminated.

Niobium with a content of up to about 0.9% by weight (preferably at least about 0.4% by weight) is preferably used as the alloy additive, the niobium being predominantly excreted as niobium carbide in the finely dispersed distribution. The niobium content can in particular be between 0.6 and 0.9% by weight, advantageously between 0.7 and 0.85% by weight.

A carbon content of less than about 0.06% by weight, advantageously about 0.04% by weight, can be provided. A concentration ratio of niobium and carbon of about 10: 1 to 30: 1 is preferred.

The carbide precipitates advantageously have a diameter between approximately 20 nm and 250 nm with an approximately spherical shape and / or up to 750 nm needle-like shape. The diameters are obtained according to the US standard ASTM E 112 by optical determination of the intercept lengths in electron microscopy

High magnification images determined.

An advantageous upper limit for the silicon content is 0.1% by weight, with tests with a maximum silicon content below about 0.08% by weight showing good results.

The total content of phosphorus and sulfur should be less than 0.03% by weight, preferably less than 0.02% by weight. Good results are achieved if the phosphorus and sulfur contents are each below 0.008% by weight.

The invention provides for steel parts and workpieces to be produced from such austenitic steel as steel, which are to be used in the radiation area of nuclear reactors. Intermediate treatments at elevated temperatures are often required for the further processing of blanks which are formed by the aforementioned rough deformation, for example for drawing or pilgrimage of the blank, in order to cure structural defects which arise between the individual processing steps and make further processing more difficult. Frequently - especially in the case of thick sheet metal parts - hot deformations are also carried out, for example rolling the glowing blank. In order to produce an austenitic steel for use in the radiation area of a nuclear reactor, a solidified melt of starting materials with the reduced content of Si, P and S and an alloyed carbide former is subjected to a temperature treatment in which a carbide formed from the carbide former is precipitated in a finely dispersed distribution . Annealing at temperatures between approximately 1000 and 1100 ° C., preferably standard annealing at approximately 1050 ° C., can be sufficient as a temperature treatment, provided that a structure of the steel is achieved in which the grains have an average diameter with an intercept length (corresponding to US -Standard ASTM-E 112) below about 20 μm. This is the case, for example, with a niobium content between about 0.4 and 0.9% by weight, it being possible for a small part of the precipitated carbide to be present in a coarser distribution. Preferably, however, to set the finely dispersed distribution, at least one high-temperature annealing (for example at approximately 1150 ° C.) can also be carried out in the coarser carbide precipitates, and only a low-temperature treatment (in particular at temperatures below approximately 800 ° C.) on this high-temperature annealing ) is carried out with at least one stabilizing annealing for adjusting the finely dispersed distribution (in particular annealing at approximately 750 ° C.). These anneals can also be combined with the desired mechanical processing steps in the form of corresponding hot deformations (eg rolling the glowing blank). The production of the corresponding semifinished product usually starts from a blank, the production of which has already reached temperatures above approximately 1100 ° C. In the prior art, further annealing is considered necessary for the further processing of the blank, which is carried out at approximately 1050 ° C. ( "Standard annealing") in order to compensate for inhomogeneities in the blank or other structural defects that could lead to cracking or bursting during subsequent drawing, extrusion or similar mechanical processing. The structure of the material sought limits the temperatures available for this processing, with a reduction the temperatures used in the intermediate annealing can be compensated for by a correspondingly longer annealing time.

The reduced content of silicon, phosphorus and sulfur is advantageously reduced by a cleaning process for the starting materials or the melt formed from the starting materials. The cleaning can be done in particular by a single or multiple melting or remelting

Vacuum. The use of a protective gas (e.g.

Argon) may be possible and is particularly advantageous for intermediate annealing. For the purity, a silicon content below 0.1% by weight and a common content of phosphorus and sulfur below 0.03% by weight are advantageous. The C content should not exceed about 0.06% by weight; As a rule, C contents between 0.03 and 0.05% by weight are permitted.

As an alloyed carbide former, niobium with a content of up to 0.9% by weight is advantageously used and a ratio of Ni ob to carbon is set approximately in the ratio 10: 1 to 30: 1. In the case of commercial austenitic steel grades, as described, for. B. were mentioned initially, usually occurs with a grain structure Grain diameters that increase to values of 50 μm and above, the better they are cleaned of Si, P and S. In the unirradiated state, they are not only against uniform

(abrasive) corrosion resistant, but also due to their high ductility against stress corrosion cracking. They survive when unirradiated, e.g. relative elongations dL up to 30% without damage. Therefore e.g. closed pipes can be expanded by increasing their internal pressure by a considerable relative change in diameter dD. This occurs e.g.

when the filling of these tubes swells and presses against the tubes from the inside, as is the case with cladding tubes, e.g. are filled with nuclear fuel or absorber material.

However, after this material has been exposed to a higher neutron flux for a longer period of time, the limit values for the relative longitudinal expansion or the relative diameter change dD, which are still undamaged, decrease. Limit values dD of only about 0.5% are typical, these values being scattered. The reasons for this scattering can be uncontrolled impurities or deviations in the grain structure which lie within the predetermined maximum values and which are based on coincidences in the respective production process and are unknown. The observed decrease in ductility is caused by a growing susceptibility to radiation-induced stress corrosion cracking and leads to the fact that austenitic steel can only be used to a limited extent in nuclear reactors.

In contrast, the material according to the invention still has sufficient ductility even after exposure to neutrons. For example, can be achieved that values dD = 1.5% or higher are still reliably survived without destroying the workpiece.

The invention is explained in more detail on the basis of an extensive series of tests with materials which are given in Tables 1, 2 and 3 and 16 figures. Show it Table 1 the chemical compositions of various

Alloys of the test series,

Table 2 shows the temperature treatments and grain sizes of these

Materials,

Table 3 the chemical composition of other successful

tested steels,

FIG. 1 shows a pipe made of these materials and made for the test series and filled with swellable material, FIG. 2 to 4 the dependence of the grain size on the temperature treatment for materials of the same composition, FIG. 5 the relationship between grain size and grain interface, FIG. 6 the ductility achieved after various temperature treatments,

FIG. 7 and 8 the change in grain size compared to FIG. 4

with the same temperature treatment but different niobium content,

FIG. 9 to 11 the formation of non-metallic precipitates and precipitates of intermetallic compounds in the structures of FIGS. 4, 7 and 8,

FIG. 12 to 14 the precipitations of niobium carbides occurring in the structures of FIGS. 9 to 11,

FIG. 15 the ductility and

FIG. 16 the dependence of ductility on the grain size. In the series of experiments, a tube shown in FIG. 1 was used, the wall 10 of which consists of one of the materials described below and which is filled with tablets made of an Al ₁ O ₃ / B ₄ C mixture. The mixing ratio is selected differently, so that these mixtures show different volume increases after they have been exposed to a predetermined neutron flow. The fluence at this neutron load was changed between 1.33 and 2.5 10 ²¹ cm ^-2 , whereby different, up to 1.7% increasing relative diameter changes are achieved. If the pipes survive these expansions without damage, in particular without stress corrosion cracking, they have passed the test on the other hand, such damage, they fail and are classified according to the maximum elongation at which no damage can yet be observed. For the manufacture of these pipes, materials are obtained from materials that are sourced as high-purity materials and that contain little or no scrap

Melt made. Advantageously and especially with a higher proportion of scrap, the melts in the arc are remelted several times under vacuum in order to achieve the lowest possible silicon, phosphorus and sulfur content.

The electrode blocks obtained in this way are forged when they cool and are extruded with blanks in the resistance furnace to give blanks of approximately 19 cm inside diameter and 22 cm outside diameter. This rough deformation is followed by a fine deformation in which the tubes are drawn to the tube section shown in FIG. 1 with repeated intermediate annealing. The intermediate annealing takes place in an induction furnace under an argon atmosphere at controlled annealing temperatures.

From the material produced in this way, sample cross sections in the unetched and etched state are examined optically and in a electron microscope using various conventional methods. The composition of the respective metal content is also determined for different grain areas and inclusions. In Table 1 are the chemical for different blanks

Compositions indicated and identified by appropriate alloy numbers. Except for the differently set niobium content, the alloys of numbers 460, 463, 480, 964, 965 and 966 correspond to steel 1.4550 or AISI 348, while alloy no. 491 corresponds to steel 1.4306 or AISI 304. The blanks formed from these alloys and identified by the corresponding alloy numbers are processed into cladding tubes, which differ essentially in the different annealing temperatures and annealing times between the individual processing steps of the fine forming and are identified in capital letters in Table 2. In the first line, the samples obtained in a low temperature process ("LTP") are listed and sorted to the right according to the decreasing niobium content. With this

Low-temperature processes are carried out after rough shaping three to five intermediate anneals at temperatures of about 850 ° C and annealing times of 240 minutes and the finished

Cladding tube is subjected to a final anneal at 850 ° C for 60 minutes.

The next line gives samples for some alloys that were obtained in a standard process, with all intermediate annealing after coarse deformation at 1065 ° C for 10 minutes. A higher temperature (1,025 ° C) and a duration of 5 minutes were also used for the final annealing.

Below this are further samples in which the intermediate annealing was carried out at several temperatures within the specified temperature ranges. The annealing time (2 minutes for this intermediate annealing) is also specified. The final annealing temperature (between 1,075 ° and 1,079 ° C) and the duration (2 or 3 minutes) are also given for these samples. The samples are therefore practically also a standard annealing process, but the temperatures of which increase slightly above the usual annealing temperature of 1,050 ° C.

Sample Q given in the next line is a transition to a high temperature process. There are four intermediate anneals with temperatures between 1,068º and 1,100 ° C and 2 minutes of annealing and a final annealing for 2 minutes at 1,100 ° C.

Sample H below uses a high temperature process for fine forming (2 minute intermediate annealing at temperatures between 1138 ° and 1189 ° C) and a stable anneal at the end which is carried out at a temperature of 748 ° C for 100 hours. With regard to the effect of temperature and Nb content on the structure and corrosion resistance described below, it can be assumed that with increasing temperature and increasing homogeneity, a structure with coarser grains, that is, one

smaller total area of the grain boundaries is obtained. The disturbing impurities from Si, P and S are concentrated at these few grain boundaries and - despite the low gross content of the alloy in these impurities - promote selective corrosion. The same applies to carbon, which at these grain boundaries leads to the formation of chromium carbide and thus to a local depletion of the

corrosion-inhibiting dissolved chromium. However, segregations of niobium carbide, especially in finely dispersed distribution, act as collection points for these impurities (i.e. the remaining basic substance can be considered largely highly pure and homogeneous) and inhibit grain growth, i.e. the rest of these interfering contaminants spread over a larger area and can no longer reach high concentrations there. The invention therefore leads to a material with high

Purity and unexpectedly small grains, at the limits of which there are corrosion-inhibiting conditions.

In Table 2, in addition to the capital letters for the designation of the samples in brackets, the mean values of the grain diameters are given, which are determined by optical measurement and counting of the inter cept lengths of a representative grain population were obtained. Corresponding, reliable information is missing for samples D, C and E, since the grain sizes were determined by methods that are customary with commercial suppliers of semi-finished products and were not found to be consistent with the diameter measurement by optical measurement, which was regarded as more reliable

Micrograph proven.

It can be seen that the grain diameter increases from top left to bottom right, i.e. grain growth is less hindered with decreasing niobium content and is promoted by increasing annealing temperatures.

First consider alloy No. 964, i.e. samples F, G and H. The grain structure of these samples is shown in FIGS. 2 to 4, which, like FIGS. 7 and 8, are recorded on a scale of 200: 1.

In the sample F obtained in the standard process, the grain diameters show a distribution around an average value of 7 μm (FIG. 2) and also the sample G produced in the low-temperature process (FIG. 4) shows approximately the same average value, the grain sizes - especially with longer ones Glow durations - have a relatively small spread. Sample H, on the other hand (FIG. 3), shows clearly enlarged grains, whose average diameter is 26 μm and which are formed by the high-temperature process.

As the grain size increases, the interface of the individual grain grows, but the number of grains decreases and thus the total of the interfaces of all grains. FIG. 5 shows the relationship between the grain diameter in μm and the total area of the grain boundaries contained in one cubic centimeter of the sample or the corresponding ASTM number.

The influence of the grain size set by changing the Nb content at different, but with approximately the same tempera Figure 6 shows samples produced by means of the expansion test in the reactor. The broken line R indicates that conventional steel grades not cleaned for Si, P and S show an IASCC susceptibility even with relative diameter changes dD of about 0.2%, which mean that the workpiece is unusable. The samples shown in Figure 6 are ordered by increasing grain diameter, the symbol "o" indicating that the corresponding elongation has been survived intact, while the symbol "(x)" minor defects and the symbol "x" serious defects which cause uselessness indicates.

From Figure 6 and Table 2 it follows that the according to

Samples produced according to the invention have an average grain diameter of approximately 20 μm and withstand relative strains of up to 1.5%.

The influence of the Nb content on the grain sizes given in Table 2 is shown in FIG. 4 (sample G), FIG. 7 (sample 3) and

Figure 8 (Sample L). Figure 9 (sample G), Figure 10 (sample J) and Figure 11 (sample L) show micrographs of these materials obtained in low-temperature treatment on a scale of 1000: 1. In addition to the occasional non-metallic inclusions (eg oxides and sulfides) that are to be considered as production defects, and the islands FE made of delta-ferrite arranged in cells, there is a statistical distribution of small niobium-containing precipitates, the frequency of which decreases with decreasing niobium content of the alloy. Figures 12 (sample F), 13 (sample H) and 14 (sample G) for alloys with a high niobium content show a more detailed examination of these precipitations and their dependence on the temperature treatment. In sample F, the temperature of the standard annealing means that there is a statistically random distribution of excretions adjusted, the maximum diameter of which is between about 40 and 560 nm and which are chemically homogeneously composed. In addition to the traces of iron, chromium and nickel, it exists

Metal content of over 90% from niobium. These are niobium carbides, while practically no precipitation of intermetallic compounds of niobium and iron (or chromium or nickel) can be observed. This finely dispersed state of precipitation, which mainly consists of niobium-rich (and low-chromium) metal carbides, is typical of the material and its chemical composition.

By further increasing the temperature in the intermediate annealing (high-temperature process), coarser carbide precipitates are partially dissolved and the corresponding carbide precipitates have an approximately spherical shape with particle diameters between 20 and 50 nm.

In the case of sample H (FIG. 13), large-area, line-like microstructure regions also occur with a further finely dispersed type of excretion, which consists of very numerous, predominantly needle-shaped excretions with maximum diameters of 20 to 750 nm. Their metal content consists of over 95% niobium with residues of iron, chromium and nickel, so it is practical

also due to niobium carbide.

In the sample G (FIG. 14), a coarser niobium-rich precipitate type 1 occurs in addition to the finely dispersed niobium carbide precipitates 2, which is probably due to the remains of structures which formed during the production of the blank, bind excess niobium and not during the low-temperature process completely converted into the finely dispersed carbide. These precipitates have a stoichiometric composition of their metal content, which is between

Nb ₂ Fe ₃ and Nb ₂ Fe ₆ fluctuates, with small ones instead of iron

Traces of Cr and Ni are detectable, which indicates an intermetallic phase. They are irregularly shaped and between 0.25 and 1.5 μm in size (up to 3 μm), while the maximum diameter of the finely dispersed carbides is only between 20 and 250 nm.

The different temperature treatment also leads to different results in the elongation test under radiation. FIG. 15 repeats the results from FIG. 6, but to the left of the dash-dotted line X contains further results and materials which are indicated by a

Invention varied temperature treatment were obtained, while on the right of the line X comparison results are shown with other materials.

The chemical processes and conditions in the coolant flow of pressurized water reactors and boiling water reactors differ. While no distinction was made between the reactor types in FIGS. 6 and 15, FIG. 16 shows a summary of results in a pressurized water reactor. For the materials produced in accordance with the invention, the expansions which have been survived without damage are indicated by the symbol “o”, while the symbol “x” is used for relative changes in diameter, which led to destruction in comparison materials. The symbols "." and "+"

denote harmless and harmful changes in diameter of a commercially available steel of German material no. 1.4981, which was also used for comparison.

Other materials listed in Table 3 are also made according to the invention and practically the same

Success tested in the reactor.

For resistance to radiation-induced stress corrosion cracking, it is therefore not only the chemical composition of the material, in particular the high purity of Si, P and S (if largely independent of other impurities such as N), but also its structure produced by the temperature treatment that is essential.

Claims

1. Austenitic steel for use in the radiation area of a nuclear reactor, with a reduced silicon content,

Phosphorus and sulfur and a structure in which a carbon contained in the steel is almost completely excreted as a carbide formed from an alloy additive in a finely dispersed distribution.

2. austenitic steel according to claim 1,

a niobium content of up to about 0.9% by weight, preferably at least 0.4% by weight.

3. austenitic steel according to claim 2,

that the niobium content is between 0.6 and 0.9% by weight and the carbon content is below about 0.06% by weight, advantageously between 0.03 and 0.05% by weight.

4. austenitic steel according to claim 2 or 3,

d a d u r c h g e k e n n z e i c h n e t that that

The ratio of niobium and carbon is approximately 10: 1 to 30: 1.

5. austenitic steel according to claim 1,

d a d u r c h g e k e n n z e i c h n t that the

Carbide deposits predominantly have a diameter between approximately 20 and 750 nm.

6. Austenitic steel according to one of claims 1 to 5, g e k e n n z e i c h n e t d u r c h a silicon content below about 0.1 wt .-%, preferably below about 0.08 wt .-%.

7. Austenitic steel according to one of claims 1 to 6, characterized by a total content of impurities by phosphorus and sulfur below about 0.03% by weight, preferably below about 0.02% by weight.

8. austenitic steel according to claim 7,

d a d u r c h g e k e n n z e i c h n e t that the content of phosphorus and sulfur is each below 0.008 wt .-%.

9. Workpiece for use in the radiation region of a nuclear reactor made of an austenitic steel according to one of claims 1 to 8.

10. A method for producing an austenitic steel for use in the radiation area of a nuclear reactor, wherein a solidified melt of starting materials with a reduced content of impurities by silicon, phosphorus and

Sulfur and an alloyed carbide former is subjected to a temperature treatment in which a carbide formed from the carbide former is precipitated in a finely dispersed distribution.

11. The method according to claim 10, a cleaning process for the starting materials or the melt, in which the content of impurities of silicon, phosphorus and sulfur is reduced.

12. The method according to claim 11,

d a d u r c h g e k e n n z e i c h n e t that the melt by single or multiple remelting or melting in

Vacuum or a protective gas is cleaned.

13. The method according to claim 10,

characterized in that the silicon content is less than 0.1% by weight and the phosphorus and sulfur content is less than about 0.03% by weight.

14. The method according to claim 13, characterized in that niobium is added as a carbide former with a content between about 0.4 and 0.9 wt .-% and that the solidified melt is subjected to a temperature treatment in which annealing or hot deformation at least once Temperatures between about 1000 ° C and 1100 ° C, preferably a standard annealing at about 1050 ° C.

15. The method according to claim 13,

characterized in that niobium with a content of between 0.4% by weight (preferably between about 0.6) and 0.9% by weight and a carbon content between about 0.03 and 0.05% by weight is added as the carbide former and that the solidified melt is subjected to several temperature treatments, with annealing or hot working at least once at temperatures of about 1150 ° C and the temperature treatments carried out after this annealing or hot working being carried out at temperatures below about 800 ° C, advantageously about 750 ° C.