WO2016005724A1 - Alliage de faible ductilité - Google Patents

Alliage de faible ductilité Download PDF

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Publication number
WO2016005724A1
WO2016005724A1 PCT/GB2015/051740 GB2015051740W WO2016005724A1 WO 2016005724 A1 WO2016005724 A1 WO 2016005724A1 GB 2015051740 W GB2015051740 W GB 2015051740W WO 2016005724 A1 WO2016005724 A1 WO 2016005724A1
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WIPO (PCT)
Prior art keywords
atomic
present
alloy
range
niobium
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Application number
PCT/GB2015/051740
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English (en)
Inventor
Dominique Flahaut
Original Assignee
Doncasters Paralloy
Priority date (The priority date is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the date listed.)
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Publication date
Priority claimed from GBGB1412315.2A external-priority patent/GB201412315D0/en
Priority claimed from GB201415625A external-priority patent/GB201415625D0/en
Application filed by Doncasters Paralloy filed Critical Doncasters Paralloy
Priority to GB1621670.7A priority Critical patent/GB2542519B/en
Priority to EP15729924.9A priority patent/EP3167090A1/fr
Priority to US15/317,600 priority patent/US20170130301A1/en
Priority to CA2953240A priority patent/CA2953240C/fr
Publication of WO2016005724A1 publication Critical patent/WO2016005724A1/fr

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    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C30/00—Alloys containing less than 50% by weight of each constituent
    • 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
    • C22C38/001—Ferrous alloys, e.g. steel alloys containing N
    • 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
    • C22C38/02—Ferrous alloys, e.g. steel alloys containing silicon
    • 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
    • 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
    • C22C38/08—Ferrous alloys, e.g. steel alloys containing nickel
    • 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
    • C22C38/12—Ferrous alloys, e.g. steel alloys containing tungsten, tantalum, molybdenum, vanadium, or niobium
    • 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
    • C22C38/18—Ferrous alloys, e.g. steel alloys containing chromium
    • C22C38/40—Ferrous alloys, e.g. steel alloys containing chromium with nickel
    • C22C38/44—Ferrous alloys, e.g. steel alloys containing chromium with nickel with molybdenum or tungsten
    • 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
    • C22C38/18—Ferrous alloys, e.g. steel alloys containing chromium
    • C22C38/40—Ferrous alloys, e.g. steel alloys containing chromium with nickel
    • C22C38/48—Ferrous alloys, e.g. steel alloys containing chromium with nickel with niobium or tantalum
    • 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
    • C22C38/18—Ferrous alloys, e.g. steel alloys containing chromium
    • C22C38/40—Ferrous alloys, e.g. steel alloys containing chromium with nickel
    • C22C38/50—Ferrous alloys, e.g. steel alloys containing chromium with nickel with titanium or zirconium
    • 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
    • C22C38/18—Ferrous alloys, e.g. steel alloys containing chromium
    • C22C38/40—Ferrous alloys, e.g. steel alloys containing chromium with nickel
    • C22C38/58—Ferrous alloys, e.g. steel alloys containing chromium with nickel with more than 1.5% by weight of manganese
    • Y—GENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y02—TECHNOLOGIES OR APPLICATIONS FOR MITIGATION OR ADAPTATION AGAINST CLIMATE CHANGE
    • Y02P—CLIMATE CHANGE MITIGATION TECHNOLOGIES IN THE PRODUCTION OR PROCESSING OF GOODS
    • Y02P30/00—Technologies relating to oil refining and petrochemical industry
    • Y02P30/20—Technologies relating to oil refining and petrochemical industry using bio-feedstock
    • Y—GENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y02—TECHNOLOGIES OR APPLICATIONS FOR MITIGATION OR ADAPTATION AGAINST CLIMATE CHANGE
    • Y02P—CLIMATE CHANGE MITIGATION TECHNOLOGIES IN THE PRODUCTION OR PROCESSING OF GOODS
    • Y02P30/00—Technologies relating to oil refining and petrochemical industry
    • Y02P30/40—Ethylene production

Definitions

  • the present invention relates to a low ductility steel tube for use in chemical engineering applications.
  • the invention relates to a high strength steel tube which has low ductility at elevated temperatures.
  • Such tubes are typically used in chemical plants for transporting reactants and products.
  • One such application includes the use in plants for producing hydrogen and methanol.
  • the tubes could also be used when producing ethylene and other hydrocarbons.
  • Steam reforming is the most widespread process for the generation of hydrogen-rich synthesis gas from light carbohydrates.
  • the feed material is natural gas, mostly in the form of methane, which is ultimately converted into methanol and hydrogen using water. This is an endothermic reaction of the gas with water in the form of steam which takes place at high temperatures in catalytic tube reactors.
  • the natural gas feed is mixed with superheated steam with the appropriate ratio of steam/carbon to allow efficient conduct of the reforming process.
  • the mixture then is distributed via manifold in vertical rows of catalyst-filled reformer tubes. The mixture flows from top to bottom of the tubes and is heated from the outside through the catalyst and reacts
  • Ethylene is a basic chemical which is widely used in the production of a number of common items such as plastic packaging that are prepared by polymerisation of ethylene and ethylene derivatives.
  • the feedstock for an ethylene plant is usually ethane or other natural gases and gas liquids derived from traditional oil and gas sources.
  • the gas, principally or entirely ethane, is heated in a steam mix in order to break down the ethane into ethylene, hydrogen and other by-products. This process is known as cracking.
  • Steam cracking is a petro-chemical process which, in general terms, saturated hydrocarbons are broken down into smaller, frequently unsaturated, hydrocarbons and hydrogen. This process represents the principal industrial method for producing lighter alkenes for subsequent use in a variety of chemical processes. Naphtha cracking represents the dominant source of ethylene globally, although gas cracking has recently become more important. Irrespective of the exact nature of the feedstock and of the chemical process used to produce ethylene and other olefins, the cracking process is invariably conducted at elevated temperatures and these are typically in the region of 800 to 1 100°C.
  • Pipes of this type are generally prepared by a centrifugal casting process. Centrifugal casting is a well-established process that is used to cast thin-walled cylinders, pipes and other axially symmetric objects. One benefit of this process is that it allows precise control of the metallurgy and crystal structure of the alloy product. It is generally used for casting iron, steel, stainless steels and alloys of aluminium, copper and nickel.
  • the centrifugal casting process employs a permanent mould which is rotated about its axis at high speeds of typically 300 to 3000 rpm as the molten metal is poured.
  • the molten metal is centrifugally thrown towards the inside mould wall where it is able to solidify after cooling.
  • the resulting cast cylinder i.e. tube, has a fine grain and the surface roughness of the outer surface of the cylinder is relatively low.
  • the internal surface has slightly more impurities and inclusions but may be subject to machining to modify the surface roughness and / or geometry.
  • JP64-031931 describes the production of a curved tube made of heat-resistant alloy.
  • the tube is prepared by centrifugal casting and the alloy of JP64-031931 is made from high strength and heat-resistant cast steel containing 15 to 30% chromium, 20 to 40% nickel as well as the optional inclusion of smaller quantities of manganese and molybdenum. Small quantities of niobium and titanium are also added to the alloy.
  • the cast tube is then subjected to the further step of an aging treatment at a temperature of from 700 to 1 100°C to deposit secondary carbide within the grain structure.
  • This patent does not attempt to control the primary carbide formation or to control the relative amounts of niobium and titanium, or carbon and nitrogen.
  • WO2012/121389 discloses an alloy intended for use in nuclear applications such as in heat exchanges in pressurised water reactors.
  • the material is said to have excellent thin workability and corrosion resistance.
  • This material is based on a nickel-chromium- iron alloy and contains small amounts of manganese, titanium, and optionally aluminium as alloying elements.
  • EP1679387 discloses a heat-resistant cast steel which has good high-temperature strength, aged ductility and creep rupture strength for use as a material in steam reforming reaction tubes in fuel cell hydrogen generation systems.
  • the cast steel contains chromium and nickel, together with manganese, niobium, titanium and cerium as alloying elements.
  • the present invention aims to provide pipes which are creep-resistant i.e. pipes which have a low ductility compared to other steel alloys at elevated temperatures.
  • a further aim is to provide low ductility alloy steels which can be produced in normal atmospheric conditions i.e. in air and to be prepared either in a reduced pressure atmosphere or in an inert atmosphere. This represents a considerable processing and economic advantage.
  • the invention aims to provide a more economic production method and/or which is also more economic when the whole of life use and maintenance interruptions are considered.
  • It is also an aim of the present invention to provide a steel alloy which is economical to manufacture and which avoids or reduces the need for expensive alloying components.
  • a further aim is to produce pipes which have high strength and / or are high in toughness. Another aim is that the pipes should have a good "shelf-life". Long term exposure under high temperature conditions can be quite detrimental to conventional steel alloys used in such applications.
  • a further aim is to produce steel alloys which have good high-temperature strength over an extended period of time.
  • a further aim is to provide steel alloys that have good corrosion resistance, particularly at elevated temperatures such as those found in a chemical plant. Another aim is to produce pipes in which the corrosion resistance is maintained over an extended period of time in use.
  • the invention satisfies some or all of the above aims.
  • a steel pipe comprising:
  • the total amount of niobium and one or more of a second carbide forming element selected from: titanium, hafnium, zirconium, vanadium, tungsten and molybdenum is from 0.50 to 0.91 atomic %, preferably 0.60 to 0.75;
  • the total amount of carbon plus nitrogen is in the range of 1.2 to 3.0 atomic %, preferably in the range 1.5 to 2.5 atomic %;
  • the amount [nitrogen / (the second carbide forming element(s) plus niobium)] is in the range 0.2 to 1.1 , preferably 0.4 to 1.0;
  • the alloy compositions of the present invention have a reduced propensity to suffer from stress fractures.
  • the occurrence of stress fractures and the strength and ductility of an alloy composition are generally dictated by the occurrence of dislocations and their distribution throughout the bulk material.
  • Good high-temperature strength and creep-resistance are properties which are mainly due to the precipitation strengthening of the grain interiors by alloy carbides. Precipitation strengthening is governed by the precipitate size, shape, distribution and crystallographic orientation within the surrounding matrix.
  • the steel alloys of the present invention have excellent
  • Metal carbides that normally provide the strengthening effect in steels are derived from niobium, vanadium, molybdenum and tungsten. Hafnium, zirconium and titanium are also known carbide formers. All of these elements can be classified as carbide-forming elements.
  • the principal carbide forming component in the alloys of the invention is usually niobium and the remainder of the abovementioned carbide-forming elements may be used (alone or in a combination of one or more of them) as a second carbide-forming component.
  • One important feature resides in the careful control of the total amount of the niobium and the one or more second carbide-forming elements. This total of the carbide-forming elements mentioned above is deliberately controlled to a maximum of from 0.5 to 0.91 , preferably from 0.60 to 0.91 atomic weight %. Thus the total amount of niobium together with one or more of titanium, hafnium, zirconium, vanadium, tungsten and molybdenum is never greater than 0.91 atomic weight %.
  • the niobium will be the principal part (in terms of the number of elemental atoms) of this total. Thus niobium will account for 50 atomic % of this total of the carbide-forming elements and is more usually at least 80 atomic %, and may be at least 90 atomic % or even at least 95 atomic % of the total. In some circumstances, however, the niobium may be present in an amount of less than 50 atomic % of the total.
  • the steel alloy of the invention consequently has a relatively small and dispersed carbide formation compared with known steels for similar applications. It is this feature, arising from a careful control of the metallurgical composition, which gives contributes to the improved mechanical properties.
  • a further benefit of the steel pipes of the invention is that they require no subsequent treating.
  • Classical precipitation strengthening of alloys due to carbide formation varies as a function of time at a given temperature. Initially, clusters of solute atoms form and then, eventually, precipitate forms which is largely coherent with the matrix. The precipitates strengthen the matrix because they prevent dislocation movement which in turn inhibits plastic deformation.
  • the steel alloy composition of the invention is designed to control primary carbide formation and ensure a substantially homogeneous distribution of carbide throughout the matrix. It is also designed to ensure smaller, more regular, carbide growth.
  • each of the elemental components described in the above composition plays an important role in the creep resistant steel of the present invention.
  • the combination of elements gives rise to the very low ductility i.e. high creep resistance that is observed in the case of the present invention.
  • the combination of elements also contributes to the high-temperature strength of the steel tube. This high strength and high creep resistance is manifested over an extended period of time relative to conventional alloys.
  • Carbon is an important component of the steel for providing tensile strength and resistance to creep rupture. Carbon is an essential component in the carbide formation which provides the steel of the present invention with its unique properties.
  • the carbon improves the strengthening of the alloy by precipitation of the primary and secondary carbides as follows: chromium based carbides (M7C3) and niobium carbides during solidification (primary carbides), and chromium based carbides (M23C6) and niobium carbides, niobium carbido-nitrides, niobium nitrides during ageing (secondary carbides).
  • M7C3 chromium based carbides
  • M23C6 chromium based carbides
  • niobium carbides niobium carbido-nitrides
  • niobium nitrides during ageing
  • carbon must be present in an amount in the range of from 1.2 to 2.5 atomic %. Preferably, it is in the range of froml .5 to 2.5 atomic %, and more preferably it is present in an amount from 1.75 to 2.25 atomic %.
  • the total of (carbon + nitrogen) needs to be above a minimum level to allow the precipitation of minimum quantity of fine primary chromium carbides and fine secondary carbides/carbo-nitrides and also needs to be below a maximum level to avoid over saturation of the austenitic matrix, and as a consequence, loss of the beneficial effect of fast solidification and loss of the control of precipitation before and during solidification.
  • the total amount of carbon plus nitrogen is in the range of from 1.2 to 3.0 atomic%
  • Nitrogen is required because it forms austenite together with carbon and it contributes to high-temperature strength. Nitrogen allows the dilution, dispersion, and the homogenisation of the carbon. The control of the amount of nitrogen is important because it slows the precipitation of primary chromium carbides when it is added in a suitable quantity. In effect, the nitrogen helps to control the 'behaviour' of the carbon so to control its several precipitations. The nitrogen participates in the precipitation of secondary niobium carbides, niobium carbido-nitrides, and niobium nitrides during ageing.
  • the quantity of nitrogen is too large then an excessive amount of nitrides are produced which reduces the toughness of the alloy over an extended period of time.
  • Both the absolute quantity of nitrogen, and the quantity relative to carbon are important to ensure high strength.
  • the nitrogen allows control of the carbide precipitations and hence nitrogen must be added in a quantity that is controlled relative to that of carbon. Therefore, as more carbon is added so more N is needed; similarly as less carbon is added then less nitrogen is needed.
  • the nitrogen disperses the carbon in the austenitic matrix which, with fast solidification, slows down the precipitation of primary chromium carbides (M7C3) and limits the segregation of the carbon close to the primary carbides. Accordingly, in addition, the ratio
  • nitrogen/carbon must be in the range of from 0.20 to 1.00, and preferably is in the range 0.20 to 0.50 atomic %.
  • nitrogen must be present in an amount in the range of from 0.01 to 1.0 atomic %. Preferably, it is in the range of from 0.20 to 0.70 atomic %, and more preferably it is present in an amount from 0.30 to 0.50 atomic %.
  • Silicon provides the function of a deoxidiser and is usually an essential component in an austenite stainless steel. Silicon may also contribute to increasing the stability of any surface oxide film. On the other hand, if the content of silicon is too high the workability of the steel is reduced. A high Si content can also cause the formation of a detrimental phase known as the G phase which is composed of nickel, silicon and niobium (Ni16Nb6Si7). Consequently, silicon must be present in an amount in the range of from 1.0 to 3.0 atom ic%. Preferably, it is in the range of from1.45 to 1.75 atomic%, and more preferably it is present in an amount from 1.65 to 1.75 atomic %.
  • Nickel is an element which is essential in order to obtain a stable austenite structure and improves the stability of austenite and supresses the generation of the sigma phase.
  • Nickel is the austenitic stabiliser element, allowing the alloy to be generally strong at above 800C. Therefore it forms a stable matrix with the iron which allows the possible precipitation of the carbides/nitrides.
  • the lower limit of the nickel content is chosen simply for the reason that this is a sufficient amount for improving the stability of austenite with respect to the lower limits of the other elements.
  • the lower limit is 20.0 atomic %.
  • the upper limit is chosen on the grounds of economy and also with respect to the upper limits of the other alloy components.
  • nickel when present in conjunction with chromium forms a stabilised austenitic structure which imparts additional strength and resistance to oxidation at elevated temperatures. There are diminishing returns as the content of nickel rises hence the practical upper limit is around 40.0 atomic%.
  • nickel is present is in the range of from 25.0 to 35.0 atomic %, and more preferably it is present in an amount from 30.0 to 33.0 atomic %.
  • Chromium provides a well-documented and effective corrosion resistance and oxidation resistance effect. Chromium also acts as a carbide-former, ensuring the creep strengthening precipitations in the alloy. Chromium-based carbide of general formula M7C3 is formed during solidification (primary carbide formation) and chromium-based carbide of general formula M23C6 is formed during ageing
  • chromium is present in the range of from 20.0 to 30.0 atomic %, and more preferably it is present in an amount from 22.5 to 27.5 atomic %.
  • niobium in the alloy acts as a carbide forming element.
  • Niobium allows formation of stable carbides, and even more stable carbo-nitride and nitrides in the alloy.
  • Niobium carbides form during solidification (primary carbides), and niobium carbides, niobium carbido-nitrides, and niobium nitrides form during ageing (secondary carbides).
  • second carbides niobium carbides
  • titanium, or one or more of the second carbide-forming elements is to form carbides.
  • titanium is mainly intended for the formation of carbides it is also engaged in the formation of nitrides and carbo- nitrides to some degree.
  • niobium needs to be carefully controlled in order to ensure sufficient, but not too much, carbide formation.
  • the primary carbides are of the form M73C.
  • the niobium carbide which is formed gives an enhanced creep rupture strength and also contributes to maintenance of the properties of the high strength and high creep resistance steel alloy over an extended period of time.
  • niobium must be present in an amount in the range of from 0.01 to 0.90 atomic %. Preferably, it is in the range of from 0.60 to 0.80 atomic %, and more preferably it is present in an amount from 0.65 to 0.75 atomic %.
  • the ratio N/(Nb+ second carbide forming element) is also important. The quantity needs to be such that it allows the beneficial precipitation of very small secondary niobium nitrides (MN) (less than 50nm) during ageing of the alloy. Hence the amount the amount [nitrogen / (the second carbide forming element(s) plus niobium)] is in the range 0.20 to 1.10.
  • the present of excess niobium may also reduce corrosion resistance and / or oxidation resistance.
  • the total amount of niobium and one or more of: titanium, hafnium, zirconium, vanadium, tungsten and molybdenum is from 0.50 to 0.91 atomic weight %, preferably 0.60 to 0.91 atomic weight %, and is more preferably from 0.65 to 0.80 atomic %, and most preferably is from 0.70 to 0.80 atomic %.
  • Titanium is added to the alloy as a deoxidiser. Furthermore, titanium as a carbide forming element not only forms titanium carbides but is also able to form a titanium- niobium double carbide precipitate which improves creep strength. The addition of too high an amount of titanium can lead to undesirable oxide formation thereby reducing strength. Consequently, titaniumwhen present must be present in an amount in the range of from 0.01 to 0.90 atomic %. Preferably, it is in the range of from 0.01 to 0.20 atomic %, and more preferably it is present in an amount from 0.01 to 0.10 atomic %.
  • the other carbide forming elements hafnium, zirconium, vanadium, tungsten and molybdenum which taken individually and independently when present must be present in an amount in the range of from 0.01 to 0.90 atomic %.
  • any of those elements when present is present in an amount in the range of from 0.01 to 0.20 atomic %, and more preferably is present in an amount from 0.01 to 0.10 atomic %.
  • Only titanium need be present as the second carbide forming element.
  • the alloy contains onlynickel, chromium, silicon, carbon, nitrogen, niobium, manganese, and titanium with the balance being iron and incidental impurities.
  • any one of those other elements may be present as the sole second carbide-forming element and the composition would then contain only nickel, chromium, silicon, carbon, nitrogen, niobium, manganese, and one of the other second carbide-forming elements described above with the balance being iron and incidental impurities.
  • niobium and titanium The double carbide formation of niobium and titanium is the reason for the careful control of the total amount of niobium and titanium and / or one of the other carbide- forming elements hafnium, zirconium, vanadium, tungsten and molybdenum. Each of those other carbide-forming elements is able to function in a similar way to titanium in forming carbides which contribute to enhanced creep rupture strength. Similar considerations apply, in terms of the need to avoid excess carbide formation, when using these elements hence the requirement that the upper limit of these elements is controlled to 0.90 atomic weight % either when present alone as a sole component (other than niobium) or when present in combination with one another.
  • Manganese is a required component of the steels of the present invention because it can improve the workability of the alloy. It is also an effective de-oxidant and contributes to austenite formation in the steel. The addition of too much manganese can result in a reduction in high-temperature strength and also toughness over an extended period of time. Consequently, manganese must be present in an amount in the range of from 1.0 to 3.0 atomic %. Preferably, it is in the range of from 1.0 to 2.0 atomic %.
  • Alloys according to the present invention are produced in a conventional furnace and without the need for a special atmosphere.
  • the first stage of preparing the alloy involves working out the relative proportions by weight of the various component minerals (which are the source of the various elements required in the final alloy) in order to achieve the desired amounts of the various elements which are required in the final alloy.
  • the solid minerals are added to the hot furnace. Heating is continued in order to melt all of the mineral components together and ensure a thorough mixing of the minerals in the furnace so that the elements are properly distributed within the matrix. Once melting and mixing has been achieved, any slag is decanted from the furnace in order to remove impurities and clean the bath of liquid alloy in the furnace.
  • a sample of the molten alloy is then removed from the furnace, allowed to cool and analysed by x- ray fluorescence in order to determine its elemental composition.
  • An adjustment to the composition may or may not be required at this stage to accommodate for any elemental mass loss due to volatility.
  • the composition is adjusted by the addition of further minerals as necessary, and optionally re-analysed to ensure that the desired composition has been achieved.
  • the temperature is further raised above the melting temperature to a tapping temperature in order to ensure easy pouring of the melt.
  • the mould is prepared for centrifugal casting.
  • the mould is a conventional centrifugal casting mould and this type of mould is well known to the skilled person.
  • the process of preparing the mould involves washing the mould with water/steam to clean it and to remove any old mould wash or coating that might have been used in a previous casting process.
  • the washed mould is then coated with an insulating/release agent which is required to prevent the alloy from sticking to the mould after casting.
  • a typical insulating/release agent is silica.
  • a disc of ceramic is then added to the centrifugal casting mould in the manner known in the art in order to ensure that the mould is liquid tight and ready for casting. This prevents any alloy leakage during the casting process.
  • the mould temperature is adjusted in preparation for the casting and may be in the range of 200° to 300° C.
  • the mould is then rotated at high speed to obtain usually the range of 80g to 120g, with a rotation providing 100g being typical for a centrifugal casting speed.
  • a ladle is then brought to the furnace and a desired weight of alloy is tapped off for the purposes of casting.
  • the ladle itself is preheated to a temperature in the region of 800° to 1000° C in order to minimise cooling of the alloy after pouring. Alloy is then transferred to the hot ladle.
  • a further analysis of the alloy may be performed and any microaddition of elemental components may also, optionally, be performed in order to adjust the final chemistry of the alloy if this is necessary.
  • the molten alloy in the ladle is then transferred to a pouring cup.
  • the nose of the pouring cup has previously been adjusted to ensure that it mates with and properly fits the size of the input tube for the centrifugal casting mould.
  • the level of molten alloy in the pouring cup is maintained in order to maintain adequate flow of alloy into the mould which is in effect fed by gravity. This provides a continuous flow of alloy into the mould until all of the weight of the alloy has been poured into the mould.
  • the mould is rotated at high speed i.e. maintained at the centrifugal casting speed during the process and whilst the alloy is molten.
  • the length of time the casting process takes depends ultimately on the desired thickness of the tube required and the skilled person is able to determine a suitable rotation time for a particular thickness of tube and weight of alloy.
  • the mould is gradually slowed down as the alloy cools from its solidification point.
  • a "fast" solidification process is one in which the alloy is cast and then cools at a rate of more than about 100° C per minute
  • a “slow” solidification process is one in which the alloy is cast and then cools at a rate of about 50° C or greater per minute.
  • the casting process is usually completed in less than about 10 minutes.
  • the tube is extracted after the mould stops and the process may be repeated again.
  • Alloys of the invention can be assessed by the Larson-Miller relation.
  • the Larson- Miller relation also widely known as the Larson-Miller Parameter is a parametric relation used to extrapolate experimental data on creep and rupture life of engineering materials.
  • Larson and Miller (Larson, Frank R. and Miller, James: A Time-Temperature Relationship for Rupture and Creep Stresses. Trans. ASME, vol. 74, pp. 765-775) proposed that creep rate could adequately be described by an Arrhenius-type rate equation which correlates the creep process rate with the absolute temperature. They established also that creep rate is inversely proportional to time.
  • the alloy of the present invention has a minimum stress value of 40MPa when measured at 850° C for 100,000 hours rupture time. In other words, following the Larson Miller model in our predictive test for an extended rupture time of 100,000 hours, the alloy of the present invention has a minimum stress value of 40 MPa at 850° C In a further embodiment, the minimum stress value is 30 MPa at 900° C. In another embodiment, the minimum stress value is 20 MPa at 950° C. In yet another embodiment, the minimum stress value is 15 MPa at 1000° C. In a still further embodiment, the minimum stress value is 10 MPa 1050° C. In further embodiments, the alloy will exhibit creep properties such that it satisfies to or more of the above minimum stress values taken in any combination. In a particularly preferred embodiment, the alloy of the present invention has creep properties in which the minimum stress is the same as or higher in the range from 900° C to 1050° C than the line represented by H39WM in Figure 3.
  • Creep strength can be measured in accordance with the standard industrial test ASTM E139-1.
  • the steel tubes of the present invention show excelled high-temperature strength and low ductility i.e. high creep resistance.
  • the tubes also display excellent corrosion resistance at elevated temperatures over an extended period of time. Consequently, these steels are particularly suited to use in chemical plant under demanding environments such as a reformer.
  • steel tubes according to the invention may be used in other applications such as ethylene crackers and in nuclear applications in heat exchanges and the like, such as those found in pressurised water reactors.
  • the beneficial properties of the steel alloys of the present invention arise due to the improved primary carbide precipitation and subsequent secondary carbide formation that occurs due to the carefully controlled relationships between the carbon, nitrogen and carbide forming elements in the alloys of the present invention.
  • the alloys of the present invention benefit from particularly small carbide formation and the carbides formed in the steels of the present invention are longer and thinner than those in comparable nickel chromium steels.
  • the standard H39WM alloy contains 25% by weight chromium, 35% by weight nickel, 1 % by weight niobium and 0.4% by weight carbon together with micro additions of other alloying elements and this alloy has a chromium carbide (present as Cr3C 7 ) present in an amount of 74%, based on a fraction analysis of a photo at 200 times magnification. In the alloys of the present invention this is found at levels around 61 %.
  • the niobium carbide content in the traditional H39WM alloy is typically about 26% whereas in the alloys according to the present invention it is around 39%, based on a fraction analysis of a photo at 200 times magnification.
  • An important feature of the alloys of the present invention is that they have a more homogeneous carbide formation. In other words, the carbides that are formed are more similar in size to one another and are smaller than in the conventional alloys. Thus, not only do the alloys of the present invention contain smaller carbides in otherwise apparently similar alloy compositions but also contain a greater proportion of niobium carbide. A lower limit of 30%, and more preferably 35% of niobium carbide as a proportion of the total amount of carbide present is preferred.
  • a maximum proportion of 70%, and more preferably a maximum of 65% of the total carbides present is represented by chromium carbide.
  • these figures refer to a fraction analysis of a photo at 200 times magnification.
  • the presence of smaller and more dispersed carbides in the present invention improve the creep resistance of the steel because the growth of secondary carbides over time reduces the ability to stop movement of dislocations. This in turn means that the steel would become weakened over time.
  • the fast precipitation of niobium from the melt during the centrifugal casting process allows the alloy compositions of the present invention to be cast with the homogeneous carbide formation and relatively larger proportion of niobium carbides to chromium carbides as compared with convention steel alloys.
  • a further important feature of the alloys of the present invention relates to the amount of secondary chromium carbides on the surface.
  • the surface fraction of Cr3C 7 is about 4% whereas in the alloys according to the invention it is at least 6% and more preferably 8% based on a fraction analysis of a photo at 200 times magnification.
  • Figures 1 to 4 show the properties of the steels H39WM (a conventional steel alloy) and H39WM+ (a steel alloy according to the invention).
  • Figure 1 shows the
  • Figure 5 shows the constant stress creep test at 950° C.

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  • Chemical & Material Sciences (AREA)
  • Engineering & Computer Science (AREA)
  • Materials Engineering (AREA)
  • Mechanical Engineering (AREA)
  • Metallurgy (AREA)
  • Organic Chemistry (AREA)
  • Heat Treatment Of Steel (AREA)
  • Organic Low-Molecular-Weight Compounds And Preparation Thereof (AREA)
  • Production Of Liquid Hydrocarbon Mixture For Refining Petroleum (AREA)
  • Heat Treatment Of Articles (AREA)

Abstract

La présente invention concerne un tube en acier de faible ductilité destiné à être utilisé dans des applications de génie chimique. En particulier, l'invention concerne un tube en acier à haute résistance qui a une faible ductilité à des températures élevées. De tels tubes sont généralement utilisés dans des usines chimiques pour le transport de réactifs et de produits. Une telle application comprend l'utilisation dans des usines pour la production d'hydrogène et de méthanol. Les tubes pourraient également être utilisés lors de la production d'éthylène et d'autres hydrocarbures.
PCT/GB2015/051740 2014-07-10 2015-06-12 Alliage de faible ductilité WO2016005724A1 (fr)

Priority Applications (4)

Application Number Priority Date Filing Date Title
GB1621670.7A GB2542519B (en) 2014-07-10 2015-06-12 Low ductility alloy
EP15729924.9A EP3167090A1 (fr) 2014-07-10 2015-06-12 Alliage de faible ductilité
US15/317,600 US20170130301A1 (en) 2014-07-10 2015-06-12 Low ductility alloy
CA2953240A CA2953240C (fr) 2014-07-10 2015-06-12 Alliage de faible ductilite

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GB1412315.2 2014-07-10
GBGB1412315.2A GB201412315D0 (en) 2014-07-10 2014-07-10 Low ductility alloy
GB1415625.1 2014-09-04
GB201415625A GB201415625D0 (en) 2014-09-04 2014-09-04 Low ductility alloy

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Cited By (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
US10501831B2 (en) * 2014-10-08 2019-12-10 L'Air Liquide, Société Anonyme pour l'Etude et l'Exploitation des Procédés Georges Claude Method for producing an alloy for a reforming tube
US11859267B2 (en) 2016-10-12 2024-01-02 Oxford University Innovation Limited Nickel-based alloy

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GB1544614A (en) * 1977-05-04 1979-04-25 Abex Corp Iron-chromium-nickel heat resistant castings
JPS57116744A (en) * 1981-01-12 1982-07-20 Kubota Ltd Heat resistant cast steel
JPS5864360A (ja) * 1981-10-12 1983-04-16 Kubota Ltd 耐熱鋳鋼
EP0391381A1 (fr) * 1989-04-05 1990-10-10 Kubota Corporation Alliage réfractaire
EP1679387A1 (fr) * 2003-10-20 2006-07-12 Kubota Corporation Acier moule resistant a la chaleur destine a des tubes de reaction pour la production d'hydrogene a tenacite au vieillissement et a resistance a la rupture en fluage excellentes

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JPS596907B2 (ja) * 1981-01-12 1984-02-15 株式会社クボタ 耐熱鋳鋼
JPS57140643A (en) * 1981-02-25 1982-08-31 Kubota Ltd Coated pipe for reactor subjected to pyrolysis and reforming of hydrocarbon
CA1190771A (fr) * 1981-04-27 1985-07-23 Junichi Sugitani Alliage resistant a la chaleur, ayant d'excellentes proprietes quant a la ductilite et se pretant bien au cintrage apres vieillissement, et produits derives dudit alliage
JPS58198587A (ja) * 1982-05-14 1983-11-18 Kubota Ltd 炭化水素類の熱分解・改質反応用管
JPH03240930A (ja) * 1990-02-16 1991-10-28 Kubota Corp 耐浸炭性および溶接性にすぐれた耐熱合金
FR2939808B1 (fr) * 2008-12-16 2011-01-07 Air Liquide Alliages fer-nickel-chrome stables a haute temperature

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Publication number Priority date Publication date Assignee Title
GB1544614A (en) * 1977-05-04 1979-04-25 Abex Corp Iron-chromium-nickel heat resistant castings
JPS57116744A (en) * 1981-01-12 1982-07-20 Kubota Ltd Heat resistant cast steel
JPS5864360A (ja) * 1981-10-12 1983-04-16 Kubota Ltd 耐熱鋳鋼
EP0391381A1 (fr) * 1989-04-05 1990-10-10 Kubota Corporation Alliage réfractaire
EP1679387A1 (fr) * 2003-10-20 2006-07-12 Kubota Corporation Acier moule resistant a la chaleur destine a des tubes de reaction pour la production d'hydrogene a tenacite au vieillissement et a resistance a la rupture en fluage excellentes

Cited By (2)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
US10501831B2 (en) * 2014-10-08 2019-12-10 L'Air Liquide, Société Anonyme pour l'Etude et l'Exploitation des Procédés Georges Claude Method for producing an alloy for a reforming tube
US11859267B2 (en) 2016-10-12 2024-01-02 Oxford University Innovation Limited Nickel-based alloy

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EP3167090A1 (fr) 2017-05-17
CA2953240A1 (fr) 2016-01-14
GB201621670D0 (en) 2017-02-01
GB2542519A8 (en) 2017-03-29
US20170130301A1 (en) 2017-05-11
CA2953240C (fr) 2023-08-01
GB2542519B (en) 2020-04-08
GB2542519A (en) 2017-03-22

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