EP1427866B1 - Verfahren zur herstellung von geschweissten röhren und dadurch hergestelltes rohr - Google Patents

Verfahren zur herstellung von geschweissten röhren und dadurch hergestelltes rohr Download PDF

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Publication number
EP1427866B1
EP1427866B1 EP02777430A EP02777430A EP1427866B1 EP 1427866 B1 EP1427866 B1 EP 1427866B1 EP 02777430 A EP02777430 A EP 02777430A EP 02777430 A EP02777430 A EP 02777430A EP 1427866 B1 EP1427866 B1 EP 1427866B1
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European Patent Office
Prior art keywords
alloy
strip
temperature
carbon
manganese
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EP02777430A
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English (en)
French (fr)
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EP1427866A1 (de
Inventor
Nicolas Guelton
Jean-Hubert Schmitt
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ArcelorMittal France SA
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USINOR SA
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    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C38/00—Ferrous alloys, e.g. steel alloys
    • C22C38/04—Ferrous alloys, e.g. steel alloys containing manganese
    • B—PERFORMING OPERATIONS; TRANSPORTING
    • B21—MECHANICAL METAL-WORKING WITHOUT ESSENTIALLY REMOVING MATERIAL; PUNCHING METAL
    • B21C—MANUFACTURE OF METAL SHEETS, WIRE, RODS, TUBES OR PROFILES, OTHERWISE THAN BY ROLLING; AUXILIARY OPERATIONS USED IN CONNECTION WITH METAL-WORKING WITHOUT ESSENTIALLY REMOVING MATERIAL
    • B21C37/00—Manufacture of metal sheets, bars, wire, tubes or like semi-manufactured products, not otherwise provided for; Manufacture of tubes of special shape
    • B21C37/06—Manufacture of metal sheets, bars, wire, tubes or like semi-manufactured products, not otherwise provided for; Manufacture of tubes of special shape of tubes or metal hoses; Combined procedures for making tubes, e.g. for making multi-wall tubes
    • B21C37/08—Making tubes with welded or soldered seams
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D8/00—Modifying the physical properties by deformation combined with, or followed by, heat treatment
    • C21D8/10—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of tubular bodies
    • C21D8/105—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of tubular bodies of ferrous alloys
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D6/00—Heat treatment of ferrous alloys
    • C21D6/005—Heat treatment of ferrous alloys containing Mn
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D8/00—Modifying the physical properties by deformation combined with, or followed by, heat treatment
    • C21D8/02—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips
    • C21D8/0221—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips characterised by the working steps
    • C21D8/0226—Hot rolling
    • C—CHEMISTRY; METALLURGY
    • C21—METALLURGY OF IRON
    • C21D—MODIFYING THE PHYSICAL STRUCTURE OF FERROUS METALS; GENERAL DEVICES FOR HEAT TREATMENT OF FERROUS OR NON-FERROUS METALS OR ALLOYS; MAKING METAL MALLEABLE, e.g. BY DECARBURISATION OR TEMPERING
    • C21D8/00—Modifying the physical properties by deformation combined with, or followed by, heat treatment
    • C21D8/02—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips
    • C21D8/0247—Modifying the physical properties by deformation combined with, or followed by, heat treatment during manufacturing of plates or strips characterised by the heat treatment
    • C21D8/0273—Final recrystallisation annealing

Definitions

  • the invention relates to iron and steel industry. More specifically, it concerns the manufacture of welded tubes, generally of small dimensions, this manufacture ending with a definitive shaping step by stretching or hydroforming.
  • a wide variety of steel grades can be used for make welded tubes of small dimensions, that is to say a few centimeters in diameter, typically 2 to 10 cm, and a few millimeters thickness, typically of the order of 5 mm.
  • carbon and carbon steels are usually used.
  • low-end manganese For more demanding applications for example, for the automotive market, more complex steels are used.
  • the exhaust lines for example, are made of steel stainless steel, ferritic or austenitic, whose properties are adjusted in playing on the conditions of annealing, hardening and drawing, or steel aluminized carbon.
  • the structural parts of automobiles, trucks and of railway material are conventionally made of carbon-manganese steels high strength ferrito-pearlitic structure with up to 0.2% carbon and 1.5 to 2% of manganese, these steels being stretched then a normalization annealing. It is also possible to use rolled steels hot high strength ferritic-bainitic structure or rolled steels dual-phase hot-rolled ferritic-martensitic structures, or cold dual-phase. All these steels can reach high prices, less because of the cost of their raw material than the cost of multiple operations annealing and shaping they must undergo.
  • the object of the invention is to provide manufacturers and users of small welded tubes, particularly in the automobile industry, a process for economic manufacture resulting in the production of products with high mechanical characteristics.
  • the carbon content of the alloy is between 0 and and 1.2% and the manganese content of the alloy is between 10 and 35%.
  • the carbon content of the alloy is between 0.2 and 1.2%, and the manganese content of the alloy is between 10 and 30%.
  • the carbon content of the alloy is included between 0.2 and 0.8%, and the manganese content of the alloy is between 15 and 30%.
  • the carbon content of the alloy is between 0.4 and 0.8%, and the manganese content of the alloy is between 20 and 24%.
  • Hot rolling may be preceded by reheating a temperature not exceeding 80 ° C below the temperature of solidus of the alloy.
  • Hot rolling may be preceded by reheating a temperature at which the precipitation of nitrides is not caused aluminum.
  • the end temperature of hot rolling is preferably greater than or equal to 900 ° C.
  • the winding temperature after hot rolling is preferably less than or equal to 450 ° C.
  • Annealing followed by over-tempering of the strip wound hot-rolled said annealing being effected under conditions allowing the resetting of carbides and avoiding their precipitation at cooling.
  • cold rolling of the strip can be carried out with a minimum reduction rate of 25%, preceded by stripping.
  • the rate of reduction of the thickness of the strip during the first cold rolling of the web is preferably at least 25%.
  • the subject of the invention is also a welded tube produced by the previous process.
  • the invention consists first of all in using a iron-carbon-manganese alloy of determined composition, and to subject it to a series of thermomechanical treatments, before its form of tubes, which provide the desired mechanical properties.
  • These alloys have, in fact, a strong work hardening capacity which allows them to associate, at the end of these treatments, a very high resistance (up to 1200 MPa) at high ductility (resulting in a high elongation at break up to 90%). They present the desired characteristics for the production of small tubes such as those used by the automobile industry to build, thanks to their resistance high, reinforcing parts of the vehicle structure, such as bars anti-intrusion integrated doors. Their ductility reserve makes them also suitable for use in forming side members, which must be capable of absorbing high deformation energy.
  • Carbon and manganese contents are included respectively between 0 and 2% and 10 and 40%, preferably respectively between 0 and 1.2% and 10 and 35%., very preferably respectively between 0.2 and 1.2% and 10 and 30%, very advantageously respectively between 0.2 and 0.8% and 15 and 30%, and optimally respectively between 0.4 and 0.8% and 20 and 24%;
  • the silicon content must be less than or equal to 5%, preferably less than or equal to 1%, optimally less than or equal to 0.5%.
  • the sulfur content must be less than or equal to 0.3%, preference less than or equal to 0,05%, optimally less than or equal to 0.01%.
  • the phosphorus content must be less than or equal to 0,1%, preferably less than or equal to 0.05%.
  • the aluminum content must be less than or equal to 5%, preferably less than or equal to 0.1%, optimally less than or equal to 0.03%.
  • the nitrogen content is less than or equal to 0.2%, preferably less than or equal to 0.1%, optimally less than or equal to 0.05%.
  • the nickel content must be less than or equal to 5%, preferably less than or equal to 2%.
  • the molybdenum content must be less than or equal to 5%, preferably less than or equal to 1%.
  • the cobalt content must be less than or equal to 3%, preferably less than or equal to 1%.
  • the tungsten content must be less than or equal to 2%, preferably less than or equal to 0.5%.
  • niobium and vanadium must each be lower or equal to 1%, preferably less than or equal to 0.1%.
  • the chromium and copper contents must each be lower or equal to 5%, preferably less than or equal to 1%.
  • the tin content must be less than or equal to 0.5%, preferably less than or equal to 0,1%.
  • the titanium content must be less than or equal to 1%, preferably less than or equal to 0,1%.
  • alloys can also tolerate maximum boron content 0.1%, preferably not more than 0.01%, a maximum calcium content or magnesium of 0.1%, preferably not more than 0.01%, arsenic or antimony maximum of 0,1%, not more than 0,05%.
  • the upper bounds that have been laid correspond to which, for certain elements, are beginning to be harmful to properties of the alloy. This is, for example, the case for aluminum and sulfur. For other elements, it is essentially economic criteria that have such upper bounds. Thus, there would be little metallurgical drawbacks to add more than 5% nickel to the alloy, but this would unnecessarily increase its cost price.
  • austenitic ferric steels and alloys have many other modes of deformation, in addition to slip. Among them, if their stacking fault energy lends itself to it, there is twinning. This mode of deformation has the advantage of providing greater plastic deformation and, consequently, higher strength than those resulting from the simple sliding of dislocations. It is therefore necessary to seek conditions that are capable of activating twinning at the commissioning temperatures of the materials to be manufactured, in particular at ambient temperature for the case of motor vehicle parts, so as to obtain a great deal of work hardening capacity.
  • the possibility of obtaining a mechanical twinning is governed firstly by the chemical composition of the alloy; secondly by the temperature at which the material is located, these two parameters acting on the stacking fault energy, and finally by the grain size of the material which determines the kinetics of the twinning.
  • the excessive formation of martensite ⁇ (more than 20% of the structure) and the formation of martensite ⁇ 'at the moment of deformation are also obstacles to obtaining satisfactory mechanical properties, in particular good ductility. It is therefore important to have, before the final step of shaping the tube, by cold drawing or by hydroforming, a material having all the desirable characteristics of these points of view. The process according to the invention gives access to such materials.
  • the single figure shows the theoretical evolution of stacking fault energy in the C / Mn plane at room temperature (300 K), in the form of curves along which the stacking fault energy, expressed in mJ / m 2 , is constant.
  • Table 1 includes the chemical characteristics and (for the samples tested by the inventors, that is to say the samples E to K) mechanical samples reported in the single figure.
  • the stacking fault energy also varies in the same direction, at a rate of ⁇ 5 mJ / m 2 for a temperature variation of ⁇ 50 ° C. This feature is important if the shaping operation is to be performed at a temperature below ambient.
  • a steel having a grain size of 50 ⁇ m has a stacking failure energy of 5 mJ / m 2 less than that of a steel of similar composition having a grain size of 2 to 5 ⁇ m.
  • an alloy according to the invention is thus obtained if its carbon content is between 0 and 2%, if its manganese content is between 10 and 40%, and if, in addition, these contents obey the relation (1), so as to avoid the formation of martensite ⁇ 'during deformation at ambient temperature.
  • the sample F has a product Rm.A of less than 60,000, although its stacking fault energy is also of the order of 15 mJ / m 2 . But its carbon content is not sufficient to make it fully benefit from the phenomenon of dynamic hardening, which will be discussed later.
  • Partial replacement of manganese with carbon present therefore both economic and metallurgical benefits.
  • an addition of 0.2% carbon makes it possible to dispense with 4 to 5% of manganese with constant stacking fault energy.
  • An area still most preferred carbon and manganese content is therefore 0.2% ⁇ C ⁇ 1.2% and 10% ⁇ Mn ⁇ 30%, the relation (1) being otherwise satisfied.
  • Increasing the carbon content may, however, have disadvantages beyond a certain limit. Indeed, there is a risk that in alloys whose composition is in the preceding preferred range, a precipitation of carbides of the M 5 C 2 and M 23 C 6 type occurs during a slow cooling. Such slow cooling may be that experienced by a coiled strip after being cast directly as a thin strip or hot rolled. M 3 C carbide can also precipitate during pearlitic transformation.
  • the tape is to be wound at a relatively high temperature, so it is best not to impose a carbon content too high for steel, if you want to avoid having to proceed then to a solution annealing of the carbides followed by a annealing. In the majority of cases corresponding to the use of tools conventional industry, it will be preferable not to exceed a certain in carbon of 0.8%. In these circumstances, to compensate for the decrease in maximum carbon content compared to the previously preferred domain defined, it is necessary to raise the minimum manganese content up to 15%. We thus obtains an even more advantageous composition range where 0.2% ⁇ C ⁇ 0.8% and 15% ⁇ Mn ⁇ 30%.
  • Sample E has a stacking fault energy of 17 mJ / m 2 , but contains only 0.19% carbon. Its resistance is only 750 Mpa. A carbon content of at least 0.4% is necessary to obtain a resistance greater than 950 MPa, as shown in sample F. This increase in the minimum carbon content requires the reduction of the maximum 24% manganese if it is desired to remain at a stacking fault energy value of about 15 mJ / m 2 , and thus maintain the same degree of twinning by deformation.
  • the optimal composition range for the alloys of the invention is therefore 0.4% ⁇ C ⁇ 0.8% and 20% ⁇ Mn ⁇ 24%.
  • the carbon and manganese contents are optimal in that they provide at room temperature adequate stack fault energies of the order of 5 to 25 mJ / m 2 .
  • the shaping of the tubes is to be carried out at a temperature substantially lower than ambient, higher carbon and manganese maximum levels may be advisable for the stacking fault energy (which, as said it, decreases when the temperature drops) is kept at a level allowing a twinning is significantly observed. Therefore, in the spirit of the invention, the carbon content of the alloy can be up to 2% and the manganese content up to 40%.
  • the maximum silicon content of 5% is justified by the need to maintain good weldability to the alloy. In practice, one less than 1%, of the order of 0.5% or less, is advisable. For the high levels of silicon, weldability problems can be reduced if welding is carried out in an inert atmosphere.
  • the inclusiveness of the alloy has an influence on its resistance and its elongation at break.
  • the manganese sulphides constitute the main source of damage leading to a rupture premature. Improvement of the characteristics at break is therefore a reason additional to limit the sulfur content.
  • the need to limit the titanium, niobium and vanadium contents is due to the fact that these elements are likely to form carbonitrides which tend to slow down recrystallization by hindering the migration of joints. This is also the case for aluminum.
  • the grain size is an important parameter for setting properties mechanical properties of the material, and can be controlled by means of annealing recrystallization. For this recrystallization annealing to be fully effective, it is necessary to limit the formation of these carbonitrides.
  • chromium, nickel, molybdenum, copper, cobalt, tungsten, tin, boron, calcium, magnesium, arsenic and antimony must be maintained within the prescribed limits so that these elements do not have significant influence on the mechanical properties of the material.
  • the casting of the steel whose composition has been mentioned above can be in ingots or, preferably, continuously to obtain slabs of classical format, with a thickness of about 200 mm. he is also possible to cast this alloy in the form of thin slabs (a few cm thick) which can then undergo hot rolling in line. This process gives access to hot rolled strips of small thickness, which may possibly not subsequently undergo cold rolling. In this In this case, coarse-grained alloys are obtained (on the order of 20 ⁇ m, this value depending on the end of rolling and winding temperatures), presenting a relatively average resistance but a high ductility. It is also possible to achieve the casting of steel by a method of direct casting of thin strips, possibly being laminated hot online or offline. The application of this casting process to the casting of iron-carbon-manganese alloys (different from those of the invention) already been proposed in EP-A-1 067 203.
  • This casting step is widely known and does not show peculiarities compared to usual practices, it will not be more detailed here.
  • the hot product is then hot-rolled. casting.
  • hot rolling begins by a heating followed by a roughing which brings the ingot to the format of a classic slab.
  • reheatings should not bring the slab to a temperature above the solidus temperature of the segregated zones, under pain of causing the appearance of "burns" that prohibit any in hot form.
  • the solidus temperature of a Fe-C-Mn alloy at 0.6% of carbon and 22% of manganese is of the order of 1280 ° C.
  • Precipitation of aluminum nitrides during reheating is also preferably avoided. This precipitation hampers the migration of the joints during hot processing.
  • iron-carbon-manganese alloys concerned by the invention may be comparable in terms of the rate of reduction per pass and the time interval between passes to those usually used for stainless steels austenitic type SUS 304, given the similarities of hardness to between SUS 304 and iron-carbon-manganese alloys the invention.
  • an exit temperature of the reheating furnace of 1100 ° C, a roughing cage outlet temperature of 980 ° C, a thickness in 38.5 mm roughing cage outlet, a temperature at the entrance of the finishing cage of 912 ° C, a rolling end temperature of 910 ° C, a band thickness at the end of rolling of 3 mm, an exit speed of 259 m / s band and a winding temperature of 480 ° C.
  • the cooling itself of the order of 10 ° C / h, starts only one to two hours after winding, you have to wind the band at such a temperature that it can not be so prolonged to temperatures at which this precipitation of carbides from iron is possible.
  • the winding temperature can be deduced from TTT diagrams of the alloy concerned.
  • TTT diagrams of the alloy concerned By way of example, for an iron-carbon-manganese alloy at 0,6% of carbon and 22% of manganese, a stay of 2 hours at a temperature of 500 ° C or more and 28 hours at 450 ° C or more leads to precipitation of iron carbides.
  • the band is worn up a temperature between 1000 and 1050 ° C at a speed such that the band remains one minute above 900 ° C, and 10 to 20 s above 1000 ° C, then it is cooled at a speed of at least 5 ° C / s.
  • the quenching is carried out to the maximum of the possibilities of the line.
  • the strip can be left as it is without proceed with its cold rolling.
  • cold rolling is necessary. This cold rolling allows also to reduce the roughness of the surface of the strip, so to obtain a surface appearance compatible with use for forming parts intended to remain visible. It also increases the band's ability to be coated.
  • the band Prior to its eventual cold rolling, the band must classically be stripped.
  • this stripping can be performed in a solution of 20% hydrochloric acid at room temperature ambient, in the presence of hexamethylenetetramine as an inhibitor.
  • the cold rolling of the strip is then carried out with a rate of total reduction which is a function not only of the desired final thickness, but also of the resistance and the hardness that one wishes to obtain.
  • a rate of total reduction which is a function not only of the desired final thickness, but also of the resistance and the hardness that one wishes to obtain.
  • the resistance reaches almost 2000 MPa after 60% of reduction, and its hardness Hv 5 under the same conditions practically reaches 700.
  • a reduction rate of 30% leads to a resistance of about 1500 MPa.
  • a rolling mill can be used conventional cold, or a Sendzimir rolling mill that gives access, in three passes, at reduction rates of the order of 60-70%, including for alloys with very high strength, greater than 1500 MPa. A thickness of 1 mm for the cold-rolled sheet can thus be obtained.
  • This recrystallization annealing must be carried out by the method of continuous annealing because a basic annealing would lead to a precipitation of carbides, which we saw was undesirable.
  • This annealing can be carried out oxidizing atmosphere, followed by stripping; it can also be of the type "Bright annealing", that is to say carried out in an inert atmosphere, which makes it possible to get rid of pickling and limit surface decarburization.
  • this annealing can do follow this annealing by passing through a cold-rolling mill ("skin-pass") or planing.
  • this recrystallization annealing is performed at a temperature of 600-1200 ° C, for 1 second to 1 hour, depending the size of the grains that one wishes to obtain.
  • an iron-carbon-manganese alloy with 0.6% carbon and 22% of manganese may preferably undergo a bright annealing 800 ° C for 90s to obtain a grain size of the order of 2.5 microns.
  • the mechanical characteristics thus obtained are a maximum resistance of 1030 MPa and an elongation at break of 60%.
  • usable iron-carbon-manganese alloys in the process according to the invention may have an elongation at break of 90% or more, if a relatively low tensile strength of 600 MPa (figures obtained for a 0.2% carbon alloy, 27% manganese, with a grain size of 30 ⁇ m). But in the range compositions (0.4 to 0.8% of carbon and 20 to 24% of manganese), an elongation at break of about 50 to 60% and a tensile strength of the order of 1000 MPa for a size of grains of 5 ⁇ m, or even a tensile strength of the order of 1200 MPa for a grain size of 1 ⁇ m.
  • these alloys are distinguished by excellent weldability in particular, that they contain optimally little or very little silicon, whose oxide is difficult to reduce, and because of their structure austenitic that makes the concepts of martensitic quenchability irrelevant and / or carbon equivalent which should normally be taken into account when the use of conventional ferritic steels to form small tubes welded.
  • these alloys can easily receive a deposit uniform and adherent zinc by electrogalvanization, especially in the case where they were cold rolled.
  • the tube After slitting the sheet, shearing its shores and progressive forming to bring its edges until docking, the tube is conventionally welded by electrical resistance, laser or high frequencies. The inner and outer scraping of the bead is then carried out welding to eliminate thickness variations. These variations thick would be unfavorable to hydroforming and would damage the tool formatting.
  • This shaping of the tube can take place by cold drawing.
  • the thickness of the tube is reduced by pulling through a die which calibrates the outside diameter and, most often, on a mandrel which calibrates the internal diameter.
  • stretching can be used to shape the tubes and transform a draft of circular section into a product having another geometry.
  • the shaping can also take place by hydroforming.
  • a hollow body of more or less complex shape is manufactured in deforming a tube under the joint action of internal pressure and forces compression acting at the ends of the tube.
  • Iron-carbon-manganese alloys used in the invention have a coefficient of hardening of the order of 0.5, which is very favorable to their good behavior during hydroforming, and makes it possible to obtain pieces of complex shape which would be inaccessible by the use of more conventional steels. Only some austenitic stainless steels would likely have comparable performance.
  • iron-carbon-manganese alloys presenting the compositions indicated gives the metal a great variety behaviors, which allow either to obtain welded tubes with better mechanical characteristics than existing products, either to obtain mechanical characteristics equivalent to those of the products existing, but for a lower cost of production and / or for a quantity of subject matter brought into play less, leading to a significant reduction in the room.
  • alloy with 0.2% carbon and 27% of manganese mentioned above whose tensile elongation exceeds 90% it is possible to eliminate the anneals intermediaries, and consider increasing stitching heights.
  • the alloy at 0.6% carbon and 22% manganese whose resistance to traction is from 1000 to 1200 MPa, it allows to obtain a mass gain important on the final tube and to simplify the control of its stage of implementation. because this high strength widens the loading range by reducing the burst area during hydroforming. Finally, so general, because of their high work hardening capacity, stretching and hydroforming of the iron-carbon-manganese alloys according to the invention have also the advantage of standardizing the mechanical characteristics in every respect of the tube.

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  • Engineering & Computer Science (AREA)
  • Mechanical Engineering (AREA)
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  • Metallurgy (AREA)
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Claims (14)

  1. Herstellungsverfahren für ein geschweißtes Rohr, wobei das Herstellungsverfahren einen abschließenden Zieh- oder Hydroformungsschritt umfasst,
    dadurch gekennzeichnet, dass:
    die Verarbeitung einer Legierung mit einer Zusammensetzung vorgenommen wird, die folgende Gewichtsprozente aufweist:
    C ≤ 2 %;
    Mn im Bereich von 10 bis 40 %, wobei Mn % > 21,66 - 9,7 C %;
    Si ≤ 5 %, vorzugsweise ≤ 1 %, optimaler Weise ≤ 0,5 %;
    S ≤ 0,3 %, vorzugsweise ≤ 0,05 %, optimaler Weise ≤ 0,01 %;
    P ≤ 0,1 %, vorzugsweise ≤ 0,05 %;
    Al ≤ 5 %, vorzugsweise ≤ 0,1 %, optimaler Weise ≤ 0,03 %;
    Ni ≤ 5 %, vorzugsweise ≤ 2 %;
    Mo ≤ 5 %, vorzugsweise ≤ 1 %;
    Co ≤ 3 %, vorzugsweise ≤ 1 %;
    W ≤ 2 %, vorzugsweise ≤ 0,5 %;
    Cr ≤ 5 %, vorzugsweise ≤ 1 %;
    Nb ≤ 1 %, vorzugsweise ≤ 0,1 %;
    V ≤1 %, vorzugsweise ≤ 0,1 %;
    Cu ≤ 5 %, vorzugsweise ≤ 1 %;
    N ≤ 0,2 %, vorzugsweise ≤ 0,1 %, optimaler Weise ≤ 0,05 %;
    Sn ≤ 0,5 %, vorzugsweise ≤ 0,1 %;
    Ti ≤ 1 %, vorzugsweise ≤ 0,1 %;
    B ≤ 0,1 %, vorzugsweise ≤ 0,01 %;
    wobei der Gehalt an Ca und Mg jeweils ≤ 0,1 %, vorzugsweise ≤ 0,01 % beträgt;
    wobei der Gehalt an As und Sb jeweils ≤ 0,1 %, vorzugsweise ≤ 0,05 % beträgt;
    dann ausgehend von dieser Legierung der Guss eines Halbzeugs vorgenommen wird,
    a) entweder in Form eines Blocks, der dann einem Warmvorstreckwalzvorgang unterzogen wird, um ihn zu einer Bramme umzuformen, oder in Form einer Bramme, wobei die Bramme dann in Form eines Bandes warmgewalzt und dann aufgerollt wird;
    b) oder in Form eines dünnen Bandes,
    dann ein Abbeizen des Bands vorgenommen wird, wenn dieses oberflächenoxidiert ist;
    dann schließlich die Herstellung des geschweißten Rohrs durch schrittweises Umformen eines Blechs, das vom vorhergehenden Band abgeschnitten wird, um seine Ränder in Anlage zu bringen,
    dann durch Schweißen der Ränder,
    dann durch Entfernen der Schweißwulst,
    dann durch Kaltziehen oder Hydroformung
    vorgenommen wird.
  2. Verfahren nach Anspruch 1,
    dadurch gekennzeichnet, dass
    der Kohlenstoffgehalt der Legierung in Bereich von 0 bis 1,2 % liegt, und der Mangangehalt der Legierung im Bereich von 10 bis 35 % liegt.
  3. Verfahren nach Anspruch 2,
    dadurch gekennzeichnet, dass
    der Kohlenstoffgehalt der Legierung in Bereich von 0,2 bis 1,2 % liegt, und der Mangangehalt der Legierung im Bereich von 10 bis 30 % liegt.
  4. Verfahren nach Anspruch 3,
    dadurch gekennzeichnet, dass
    der Kohlenstoffgehalt der Legierung in Bereich von 0,2 bis 0,8 % liegt, und der Mangangehalt der Legierung im Bereich von 15 bis 30 % liegt.
  5. Verfahren nach Anspruch 4,
    dadurch gekennzeichnet, dass
    der Kohlenstoffgehalt der Legierung in Bereich von 0,4 bis 0,8 % liegt, und der Mangangehalt der Legierung im Bereich von 20 bis 24 % liegt.
  6. Verfahren nach einem der Ansprüche 1 bis 5,
    dadurch gekennzeichnet, dass
    dem Warmwalzvorgang eine Erwärmung vorausgeht, die bei einer Temperatur durchgeführt wird, welche die Solidustemperatur der Legierung um nicht mehr als 80°C unterschreitet.
  7. Verfahren nach einem der Ansprüche 1 bis 6,
    dadurch gekennzeichnet, dass
    dem Warmwalzvorgang eine Erwärmung vorausgeht, die bei einer Temperatur durchgeführt wird, bei der keine Ausscheidung von Aluminiumnitriden hervorgerufen wird.
  8. Verfahren nach einem der Ansprüche 1 bis 7,
    dadurch gekennzeichnet, dass
    die Endtemperatur des Warmwalzvorgangs höher als oder gleich 900°C ist.
  9. Verfahren nach einem der Ansprüche 1 bis 8,
    dadurch gekennzeichnet, dass
    die Aufrolltemperatur nach dem Warmwalzvorgang niedriger als oder gleich 450°C ist.
  10. Verfahren nach einem der Ansprüche 1 bis 9,
    dadurch gekennzeichnet, dass
    ein Glühen, gefolgt von einer Überhärtung des warmgewalzten aufgerollten Bandes durchgeführt wird, wobei das Glühen unter Bedingungen stattfindet, die den Wiederübergang der Karbide in Lösung ermöglichen und ihre Ausscheidung beim Abkühlen verhindern.
  11. Verfahren nach einem der Ansprüche 1 bis 10,
    dadurch gekennzeichnet, dass
    nach dem Warmwalzvorgang und dem etwaigen Glühen gefolgt von einer etwaigen Überhärtung ein Kaltwalzvorgang des Bandes mit einer Mindestreduktionsrate von 25 % vorgenommen wird, dem ein Abbeizen vorausgeht.
  12. Verfahren nach Anspruch 11,
    dadurch gekennzeichnet, dass
    die Reduktionsrate der Dicke des Bands beim ersten Durchgang des Kaltwalzvorgangs des Bandes mindestens 25 % beträgt.
  13. Verfahren nach einem der Ansprüche 11 oder 12,
    dadurch gekennzeichnet, dass.
    ein Rekristallisationsglühen des Bands bei einer Temperatur von 600 bis 1200°C für 1 Sekunde bis 1 Stunde lang vorgenommen wird.
  14. Geschweißtes Rohr,
    dadurch gekennzeichnet, dass
    es mit dem Verfahren nach einem der Ansprüche 1 bis 13 hergestellt wurde.
EP02777430A 2001-09-20 2002-09-12 Verfahren zur herstellung von geschweissten röhren und dadurch hergestelltes rohr Expired - Lifetime EP1427866B1 (de)

Applications Claiming Priority (3)

Application Number Priority Date Filing Date Title
FR0112160 2001-09-20
FR0112160A FR2829775B1 (fr) 2001-09-20 2001-09-20 Procede de fabrication de tubes roules et soudes comportant une etape finale d'etirage ou d'hydroformage et tube soude ainsi obtenu
PCT/FR2002/003116 WO2003025240A1 (fr) 2001-09-20 2002-09-12 Procede de fabrication de tubes roules et soudes comportant une etape finale d'etirage ou d'hydroformage et tube soude ainsi obtenu

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EP1427866A1 EP1427866A1 (de) 2004-06-16
EP1427866B1 true EP1427866B1 (de) 2005-11-23

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AT (1) ATE310835T1 (de)
DE (1) DE60207591T2 (de)
ES (1) ES2254752T3 (de)
FR (1) FR2829775B1 (de)
WO (1) WO2003025240A1 (de)

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CN101107377B (zh) * 2005-01-21 2011-03-23 阿塞洛法国公司 铁-碳-锰奥氏体钢板的制造方法和由此制造的板材
CN102059253A (zh) * 2011-01-17 2011-05-18 江苏共昌轧辊有限公司 整体铸钢支承辊
CN101653792B (zh) * 2009-09-22 2011-08-31 西北有色金属研究院 一种钼及钼合金窄带的加工方法
CN107557683A (zh) * 2017-08-16 2018-01-09 南京钢铁股份有限公司 一种高磷铁水生产厚壁大口径抗酸耐蚀管线钢的方法
WO2019233015A1 (zh) * 2018-06-04 2019-12-12 南京钢铁股份有限公司 一种大厚壁抗酸耐蚀管线钢及其生产方法

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FR2857980B1 (fr) * 2003-07-22 2006-01-13 Usinor Procede de fabrication de toles d'acier austenitique fer-carbone-manganese, a haute resistance, excellente tenacite et aptitude a la mise en forme a froid, et toles ainsi produites
FR2876708B1 (fr) * 2004-10-20 2006-12-08 Usinor Sa Procede de fabrication de toles d'acier austenitique fer-carbone-manganese laminees a froid a hautes caracteristiques mecaniques, resistantes a la corrosion et toles ainsi produites
FR2878257B1 (fr) * 2004-11-24 2007-01-12 Usinor Sa Procede de fabrication de toles d'acier austenitique, fer-carbone-manganese a tres hautes caracteristiques de resistance et d'allongement, et excellente homogeneite
KR20070099684A (ko) * 2005-02-02 2007-10-09 코루스 스타알 베.뷔. 고강도 및 양호한 성형성을 갖는 오스테나이트계 강, 상기강의 제조방법 및 상기 강의 용도
KR100742823B1 (ko) * 2005-12-26 2007-07-25 주식회사 포스코 표면품질 및 도금성이 우수한 고망간 강판 및 이를 이용한도금강판 및 그 제조방법
DE102006020746A1 (de) * 2006-05-04 2007-11-15 Dünne, Heinz Verschleißfestes Rohr mit Längsnaht
EP1878811A1 (de) * 2006-07-11 2008-01-16 ARCELOR France Verfahren zur herstellung eines eisen-kohlenstoff-mangan austenitischer stahlblehs mit hervorragender verzögerter bruchfestigkeit und bleh folglich hergestellt
WO2010126268A2 (ko) * 2009-04-28 2010-11-04 연세대학교 산학협력단 고강도 및 고연성을 갖는 고망간 질소 함유 강판 및 그 제조방법
EP2402472B2 (de) † 2010-07-02 2017-11-15 ThyssenKrupp Steel Europe AG Höherfester, kaltumformbarer Stahl und aus einem solchen Stahl bestehendes Stahlflachprodukt
WO2012052626A1 (fr) 2010-10-21 2012-04-26 Arcelormittal Investigacion Y Desarrollo, S.L. Tole d'acier laminee a chaud ou a froid, don procede de fabrication et son utilisation dans l'industrie automobile
CN102286704B (zh) * 2011-08-26 2013-03-06 三一重型装备有限公司 耐磨抗腐蚀高锰钢及其制备方法
CN104884661B (zh) 2012-12-26 2017-05-31 Posco公司 焊接热影响区韧性优异的高强度奥氏体类钢材及其制备方法
DE102015115726B4 (de) 2015-09-17 2018-08-02 Thyssenkrupp Ag Verfahren zum Herstellen eines Bauteils aus einem Stahlflachprodukt
DE102015117956A1 (de) * 2015-10-21 2017-04-27 Salzgitter Flachstahl Gmbh Verbundrohr bestehend aus einem Trägerrohr und mindestens einem Schutzrohr und Verfahren zur Herstellung hierfür
KR20180085797A (ko) * 2015-12-22 2018-07-27 주식회사 포스코 내수소취화성이 우수한 오스테나이트계 강재
EP3686308B1 (de) * 2018-05-23 2022-10-05 Manchao He Unmagnetisches npr-ankerstangenstahlmaterial und herstellungsverfahren dafür

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CN101107377B (zh) * 2005-01-21 2011-03-23 阿塞洛法国公司 铁-碳-锰奥氏体钢板的制造方法和由此制造的板材
CN101653792B (zh) * 2009-09-22 2011-08-31 西北有色金属研究院 一种钼及钼合金窄带的加工方法
CN102059253A (zh) * 2011-01-17 2011-05-18 江苏共昌轧辊有限公司 整体铸钢支承辊
CN107557683A (zh) * 2017-08-16 2018-01-09 南京钢铁股份有限公司 一种高磷铁水生产厚壁大口径抗酸耐蚀管线钢的方法
CN107557683B (zh) * 2017-08-16 2018-11-09 南京钢铁股份有限公司 一种高磷铁水生产厚壁大口径抗酸耐蚀管线钢的方法
WO2019233015A1 (zh) * 2018-06-04 2019-12-12 南京钢铁股份有限公司 一种大厚壁抗酸耐蚀管线钢及其生产方法

Also Published As

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DE60207591T2 (de) 2006-07-06
ATE310835T1 (de) 2005-12-15
FR2829775A1 (fr) 2003-03-21
EP1427866A1 (de) 2004-06-16
WO2003025240A1 (fr) 2003-03-27
ES2254752T3 (es) 2006-06-16
FR2829775B1 (fr) 2003-12-26
DE60207591D1 (de) 2005-12-29

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