EP1987170A1 - Alliage en aluminium presentant des proprietes d'ecrasement ameliorees - Google Patents

Alliage en aluminium presentant des proprietes d'ecrasement ameliorees

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Publication number
EP1987170A1
EP1987170A1 EP07715944A EP07715944A EP1987170A1 EP 1987170 A1 EP1987170 A1 EP 1987170A1 EP 07715944 A EP07715944 A EP 07715944A EP 07715944 A EP07715944 A EP 07715944A EP 1987170 A1 EP1987170 A1 EP 1987170A1
Authority
EP
European Patent Office
Prior art keywords
alloy
alloys
crush
extruded
extrusion
Prior art date
Legal status (The legal status 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 status listed.)
Withdrawn
Application number
EP07715944A
Other languages
German (de)
English (en)
Inventor
Trond Furu
Ulf Tundal
Jostein RØYSET
Oddvin Reiso
Current Assignee (The listed assignees may be inaccurate. Google has not performed a legal analysis and makes no representation or warranty as to the accuracy of the list.)
Norsk Hydro ASA
Original Assignee
Norsk Hydro ASA
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.)
Filing date
Publication date
Application filed by Norsk Hydro ASA filed Critical Norsk Hydro ASA
Publication of EP1987170A1 publication Critical patent/EP1987170A1/fr
Withdrawn legal-status Critical Current

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Classifications

    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C21/00—Alloys based on aluminium
    • C22C21/02—Alloys based on aluminium with silicon as the next major constituent
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C1/00—Making non-ferrous alloys
    • C22C1/06—Making non-ferrous alloys with the use of special agents for refining or deoxidising
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22C—ALLOYS
    • C22C21/00—Alloys based on aluminium
    • C22C21/06—Alloys based on aluminium with magnesium as the next major constituent
    • C22C21/08—Alloys based on aluminium with magnesium as the next major constituent with silicon
    • C—CHEMISTRY; METALLURGY
    • C22—METALLURGY; FERROUS OR NON-FERROUS ALLOYS; TREATMENT OF ALLOYS OR NON-FERROUS METALS
    • C22F—CHANGING THE PHYSICAL STRUCTURE OF NON-FERROUS METALS AND NON-FERROUS ALLOYS
    • C22F1/00—Changing the physical structure of non-ferrous metals or alloys by heat treatment or by hot or cold working
    • C22F1/04—Changing the physical structure of non-ferrous metals or alloys by heat treatment or by hot or cold working of aluminium or alloys based thereon
    • C22F1/05—Changing the physical structure of non-ferrous metals or alloys by heat treatment or by hot or cold working of aluminium or alloys based thereon of alloys of the Al-Si-Mg type, i.e. containing silicon and magnesium in approximately equal proportions

Definitions

  • the present invention relates to an Al-Mg-Si aluminium alloy having improved ductility and crush properties with good energy absorption and temperature stability, and which is particularly useful for structural components in crash exposed areas in vehicles.
  • US 4525 326 discloses an Al-Mg-Si alloy where vanadium, V, is added for improving the alloy's ductility.
  • V vanadium
  • US 4525 326 discloses an Al-Mg-Si alloy where vanadium, V, is added for improving the alloy's ductility.
  • Titanium, Ti is not' mentioned in US 4 525 326, and neither in subsequent process-specific patents by the same inventor (US 5 766 546, EP 1 104 815) where the principle of ductility improvement by adding V in combination with Mn and other elements is applied.
  • EP 0 936 278 improved ductility is claimed for Al-Mg-Si alloys with additions of V in the range 0.05-0.20 wt.% in combination with addition of Mn > 0.15-0.4 wt.%.
  • the preferred Mn/Fe ratio is 0.45 - 1.0, and more preferably 0.67 - 1.0.
  • the role of Ti in EP 0 936 278 is explicitly stated to be as a grain refiner during casting or welding. However, the preferred range for Ti is not more than 0.1 wt.%.
  • the present invention is related to aluminium alloys containing Mg and Si as the primary alloying elements.
  • the alloy according to the invention contains Ti in excess of Ti commonly added as grain refiner.
  • the alloy of the invention contains Ti in excess of the Ti-containing particles that are introduced by the grain refiner. The excess Ti contributes to improved ductility of the alloy.
  • the alloy may contain Cu for additional strength. Further, the alloy may contain Fe and jZ ⁇ as incidental impurities. Still further, the alloy may contai ⁇ ;additional alloying elements including,, but not limited;to, Mn ; , ; Qr, Zr and V for further improving the ductility of the alloy.
  • the alloy is developed for extruded products where good crush behaviour is requested.
  • the alloy is optimised for productivity and for obtaining good ductility without requiring rapid quenching of the extruded profiles at the extrusion press.
  • the alloy may also be used for other products such as rolled sheet or forgings when improved ductility is requested.
  • the invention is characterized by the features as defined in the attached independent claim 1 and dependent claims 2 -8.
  • Fig. 1 is a diagram showing the total elongation for extruded profiles of aluminium alloys with various Mg and Si contents after age hardening to maximum hardness
  • Fig. 2 shows the cross-section geometries of the extruded hollow profiles used in crush-testing in the examples in the specification
  • Fig. 3 shows the grade in crush-test and yield strength of the specimens of
  • Fig. 4 shows decrease in yield strength (YS) and ultimate tensile strength (UTS) due to thermal exposure for 100Oh at 15O 0 C of age hardened extruded profiles of the alloys O and P of Example 2 in the specification,
  • Fig. 5 shows Vickers hardness of the alloys of Table 4 in the specification as a function of ageing time at 175 0 C- and at 20O 0 C
  • Fig. 6 shows the tensile yield strength in T5 condition, and after high temperature exposure of a recrystallised 6005A 1 alloy and a non-recrystallised 6082 alloy,
  • Fig. 7 shows grade in crush-test and yield strength of the specimens of Example
  • Fig. 8 shows the yield strength and Charpy energy of the water-quenched and age hardened samples according to Example 4 in the specification
  • Fig. 9 shows grade in crush-test of the specimens of Example 4 in the specification, were the nominal contents of Mn, V, Cr, Cu and Ti of the different alloys are shown on the depicted chart,
  • Fig. 10 shows two pictures where the left picture shows the grain structure in alloy variant B1 with 0.15%Mn and 0.1% V, whereas the right picture shows the grain structure in alloy variant B3 with 0.06% Cr in addition to the elements found in alloy B1 of Example 4.
  • Fig. 11 shows the grade in crush-test of the specimens of Example 6 that were extruded to geometry P3 at an exit speed of 15m/min and where the nominal contents of Mn, V, Cr, Cu and Ti of the different alloys are shown on the depicted chart,
  • Fig. 12 shows the same as in Fig. 11 , but where the exit speed is 30 m/min and where the yield strength of the specimens is included,
  • Fig. 13 shows grade in crush-test and yield strength of the specimens of Example
  • Fig. 14 shows grade in crush-test of the specimens of Example 7 in the specification that were extruded to geometry P1 at an exit speed of 15 m/min, and then air cooled prior to age hardening, where the nominal contents of Mn, V, Cr, Cu and Ti of the different alloys are shown on the in the depicted chart,
  • Fig. 15 shows grade in crush-test of the specimens of Example 7 in the specification that were extruded to geometry P3 at an exit speed of 15 m/min, and then air cooled prior to age hardening, where the nominal contents of Mn, V, Cr, Cu and Ti of the different alloys are shown on the in the depicted chart,
  • Fig. 16 shows grade in crush-test and yield strength of the specimens of Example
  • Fig. 17 shows Charpy energy vs grade in crush-test for the specimens of Example
  • Fig. 18 shows differences in yield strength and Charpy energy between alloys of
  • Fig. 19 shows yield strength and Charpy energy of the alloys of Table 10 of the specification when the profiles were water-quenched prior to age hardening
  • Fig. 20 shows yield strength and Charpy energy of the alloys of Table 10 when the profiles were air cooled prior to age hardening.
  • Fig. 21 shows a Mg-Si diagram where the Si/Mg ratio of 1.4 is drawn, as well as alloy compositions of particular interest for embodiments of the invention as defined in the claims.
  • Alloys of the Al-Mg-Si type gain their strength from the precipitation of particles of nanometer size. It is commonly known that the hardening particles have a molar Si/Mg ratio of approximately 1 (G.A. Edwards et al., Mater.Sci. Forum vol 217-222 (1996) pp713-718), and some investigations indicate that this ratio is exactly 1.2 (SJ. Andersen et al., Acta Mater, vol. 49 (1998) pp65-75, C. Ravi and C. Wolverton, Acta Mater, vol. 52 (2004) pp4213-4227). A molar Si/Mg ratio of 1.2 equals a Si/Mg weight ratio of approx.
  • the Mg and Si content should be chosen so as to ensure that as much Mg and Si as possible is used for making hardening precipitates, or in other words so as to ensure that there is as little surplus Mg or Si as possible after precipitation hardening.
  • surplus Mg or Si it should be understood the Mg or Si that does not form precipitates.
  • the surplus Mg or Si contributes little to the strength, but has a distinct negative effect on the productivity in extrusion.
  • Si In order to find the optimal Si/Mg ratio of an alloy, one has to consider that some of the Si will be tied up in the Fe-bearing primary particles and other non-hardening particles that form during casting and homogenisation of the alloy. This Si may be considered as "lost” or without effect with respect to age hardening. One may introduce a term "effective Si content", Si eff , defined by
  • Si tot is the total Si content of the alloy and Si nhP is the amount of Si tied up-in non- hardening particles. It is not straightforward to calculate Si nhP , since this is related, both to the composition of the alloy and to the temperature history during homogenisation. However, ⁇ trs normally found that the ratio ⁇
  • the Si eff /Mg ratio should be 1.4 in order to optimise the strength of the alloy.
  • Extruded profiles of Al-Mg-Si alloys are used as structural components in crash-exposed areas of automobiles. Such components are required to absorb high amounts of energy in the event of a crash, and in order to do so they must deform without fracturing.
  • One of the means of controlling that the extruded profile has the required properties is to test it by axial crushing. In this test a specimen of thin-walled extruded profile, usually a hollow profile with one or more chambers, of pre-defined length is subjected to deformation in the longitudinal direction at a controlled speed, which reduces the specimen length to typically 30-80% of the original length.
  • Good deformation behaviour is characterised by regular folding of the specimen walls, little or no cracking of the specimens and a smooth surface of the deformed areas.
  • Poor deformation behaviour is characterised by limited folding of the specimen walls, extensive cracking or fracturing of the specimens and a rough and uneven surface of the deformed areas.
  • the deformation behaviour in axial crushing tests depends strongly on the geometry of the tested profile and to some extent also on the testing conditions. Considering the geometry, the cross-section of the profile is particularly important. One general relationship is that good deformation behaviour gets increasingly difficult when the wall thickness increases and when the chamber size decreases. Besides the geometry of the tested profile and the testing conditions there are several factors that have an impact on the deformation behaviour in a crush test including, but not limited to, grain structure, strength and ductility of the extruded profile. The strength follows primarily from the chosen Mg and Si (and Cu) content in combination with the conditions of precipitation hardening.
  • the alloys have been cast to billets by the DC casting process used in production facilities of the applicant.
  • the billets have been homogenised at temperatures between 570-580 0 C and subsequently cooled at a rate of 300-400 0 C per hour down to room temperature.
  • the preheating of the billets has been performed with an induction furnace to temperatures in the range of 490-500 0 C prior to extrusion.
  • Tests were performed with alloys as specified in Table 1 below, which are essentially equal except for the Si/Mg ratio. Hollow profiles were extruded from the alloys, with cross-sections as indicated in Figure 2 a). The reduction ratio during extrusion was 24, and the profile exit speed was 15m/min. The profiles were water-quenched at the extrusion press, aged to maximum hardness and cut to specimens of 100mm length. The specimens were reduced to 40mm length in controlled axial crushing, and the deformation behaviour was characterised and given a grade on a scale from 1 to 10. The definitions of the different grades are given in Table 2. For the evaluation of the grades, three samples were crushed for each alloy, and the grade of the alloy is the arithmetic mean of the three samples. Fig. 3 shows the grades given to the individual alloys as a function of Si/Mg ratio. Also shown in Fig. 3 is the yield strength of the different alloys.
  • alloy A1 with the highest Si/Mg ratio performs slightly poorer than the other ones and alloy B1 , with a Si/Mg ratio very close to the ideal value of 1.4, performs slightly better than the other ones.
  • the alloys C1 , D1 , E1 and F1 all gained the grade 9 in this test. Considering the strength of the alloys, one should expect the alloys with lower strength to perform better in such a test than alloys with a higher strength. Thus, taking the strength into account one may state that within the alloys C1 , D1 , E1 and F1 the performance in the crush test is improving when the Si/Mg ratio increases from 0.7 to 1.2. In conclusion, there is a benefit of choosing alloys with a Si/Mg ratio close to 1.4 also with regards to the crush test performance.
  • thermal stability refers to the ability of an alloy to retain mechanical properties after exposure to high temperatures. For Al-Mg-Si alloys it is found that within a given strength class the thermal stability is highest for an alloy with a Si/Mg ratio of approx. 1.4. This is substantiated by the following examples:
  • alloy P with a Si/Mg ratio of 1.4 has a lower loss in strength, and particular in ultimate tensile strength, than alloy O with a Si/Mg ratio of 0.9.
  • alloy P has the highest thermal stability of the two alloys.
  • the profiles should always be water-quenched after extrusion.
  • water quenching leads to distortions of the geometry of the extruded section, and the risk of distortion increases with increasing complexity of the. profile.
  • the general practice is to, cool as fast as possible without introducing geometrical distortions to the profiles.
  • the majority of the extruded sections are cooled either with forced air or with controlled water-spray.
  • Example 3 The crush behaviour of Example 3 is significantly poorer than in Example 1 , but applying water-quenching as in Example 1 will impose limitations on deliverable profile geometries and geometric tolerances. Therefore the inventors were determined to find alloys that have a crush-behaviour approaching that of Example 1 , but that can be air- cooled after extrusion. It is well known among experts that small additions of the elements Mn, Cr and V improve the ductility of air-cooled extrusions of Al-Mg-Si alloy.
  • Alloying elements for improving ductility in extruded Al-Mg-Si alloys Manganese (Mn). and Chromium (Cr) have several known purposes in the -Al-Mg-Si : extrusion alloys. Both elements form small particles, referred to as dispersoids, during the homogenisation of the cast material. When present in a sufficient number density, these dispersoids may prevent recrystallisation of the extruded material, resulting in a fibrous microstructure. For lower number densities of dispersoids the extruded material will recrystallise, but the presence of dispersoids has a positive influence on the ductility of the age-hardened material. It has been found that this influence is in part related to the texture of the material. For alloys that recrystallise after extrusion one normally finds a high degree of cube texture in the extruded profiles. The presence of dispersoids leads to a higher degree of cube texture in recrystallised extruded profiles.
  • the alloys were extruded to flat bar profiles. This generates a high degree of cube texture in the alloy material. Some material was subjected to additional thermo mechanical treatment to promote an as texture-free material as possible. The texture intensities obtained are indicated in Table 7.
  • Table 7 Texture intensities measured in the samples.
  • the second adverse effect is that increasing dispersoid density imposes increasing demands on the cooling rate after extrusion to avoid loss of hardening potential of the alloy.
  • the reason for this is that the dispersoids act as nucleation sites for non-hardening Mg-Si precipitates.
  • the third adverse effect is linked to the grain size of the extruded profile. If the number density of dispersoids is too low to prevent recrystallisation it can still prevent some nuclei from growing to recrystallised grains. With only a few grains able to grow, the result may be a very coarse grain structure in the extruded profile. Upon subsequent forming of the extruded profile the result can be extensive orange peeling.
  • Mn and Cr additions in excess of what is necessary for benefiting from improved ductility.
  • the optimal content of Mn and Cr depends strongly on processing conditions and profile geometry. For many conditions the typical additions for improving ductility are in the range 0.03 - 0.25 wt.% Mn and 0.01 - 0.15 wt.% Cr. If the two elements are combined the amount of each element may have to be reduced in order to keep the total number of dispersoids at an acceptable level.
  • Zirconium is also an alloying element that forms dispersoids during homogenisation of cast material.
  • Zr may form several types of dispersoids.
  • the dispersoid type that forms in highest number density, and thus normally is the preferred type, has a composition of AI 3 Zr and an atomic arrangement referred to as LI 2 structure.
  • LI 2 AI 3 Zr In alloys of the Al-Mg-Si system the formation of LI 2 AI 3 Zr is not always feasible, and other types of dispersoids will form.
  • the other types of dispersoids may contain Si in addition to Zr and Al.
  • the effect of Zr dispersoids on the microstructure of extruded Al alloys is primarily related to the number density and to a smaller degree related to dispersoid type.
  • V Vanadium
  • V has a documented effect in increasing the ductility of Al-Mg-Si alloys. V may form dispersoids in Al-Mg-Si alloy, but for additions of up to 0.1 wt.% and possibly higher one finds that no appreciable amount of dispersoids is formed.
  • Titanium (Ti) is normally added to Al alloys together with boron (B) or carbon (C) for the purpose of refining the grain size of the alloy during casting.
  • Ti and B or Ti and C are not added individually to the melt, but as pre-prepared Al-Ti-B or Al-Ti-C alloys.
  • the pre- prepared Al-Ti-B or Al-Ti-C alloys are commonly referred to as a "grain refiner".
  • the Al- Ti-B grain refiner often contains two classes of particles, one class consisting essentially of Ti and B and these particles are in the following denoted as (Ti 1 B) particles, and another class consisting essentially of Ti and Al and these particles are in the following denoted as (AI 1 Ti) particles.
  • the Al-Ti-B grain refiners are often characterized by the weight ratio between the Ti and B content, and the Ti/B ratio is normally in the range 2- 10.
  • the (Ti,B) and (AI 1 Ti) particles are dispersed in the melt and upon casting they act as nucleation points for aluminium grains during the solidification.
  • the Al-Ti-C. grain refiners work essentially in the same manner, except that they contain (Ti,C) particles instead of (Ti 1 B) particles.
  • Ti also has an effect on the ductility of the Al-Mg-Si alloys. This requires a Ti content in excess of what would otherwise be used for grain refinement, and it requires Ti in excess of the (Ti 1 B) and/or (Ti 1 C) particles from the grain refiner.
  • the amount of Ti required is within the range 0.03 - 0.25 wt.%, and preferably within 0.05 - 0.20 wt.%.
  • V additions of Ti up to about 0.25% will probably not produce any substantial amount of dispersoids.
  • the mechanism for improving ductility is probably the same for both V and Ti.
  • the improvement in crush performance obtained by adding Ti to an Al-Mg-Si alloy is comparable to the improvements by adding Mn, Cr or V to the alloys. This is substantiated by the following examples:
  • Table 8 Composition of the alloys of Examples 5 and 6.
  • Example 3 The same tests as that of Example 3 were performed, with cooling of the extrusions in forced air. Specimens of the age-hardened profiles were subjected to axial crush testing, and grades were given according to Table 2. The grades of the individual alloys are shown in Fig. 9.
  • extrusion reduction ratio and extrusion exit speed may vary considerably between different extruded geometries. These variations have an effect of the microstructure of the extruded profile, which in turn may have an impact on the ductility in a crush test. Further, it is known that higher strength in general leads to poorer folding behaviour in an axial crushing test. Thus several tests were performed in order to verify that the findings of Example 5 are valid for variations in processing conditions and for variations in strength.
  • GO and G5 through G9 are essentially equal to the alloys BO and B5 through G9 with the exception of the Mg and Si content.
  • the Mg and Si content of the alloys of Table 9 is somewhat higher than that of the alloys of Table 8, meaning that the alloys of Table 9 should have a somewhat higher strength than the corresponding alloys of Table 8.
  • the stronger alloys are expected to have a slightly lower ductility, and therefore also a slightly lower performance in an axial crush test.
  • the alloys were extruded under four different conditions:
  • the Charpy V-notch test is a test of a material's ability to absorb energy during failure. It is found that within groups of alloys that are somewhat similar there is a high degree of correlation between the amount of energy absorbed in a Charpy test and the behaviour in an axial crush test. This is substantiated in Fig. 17, which shows the correlation between the grades in the crush test of Fig. 16 and the absorbed energy in Charpy tests of the same material. Except for alloy GO, which shows a too low Charpy energy compared to the grade in the crush test, one finds that there is almost a linear relationship between the Charpy energy and the crush test grade for the alloys.
  • alloys as specified in Table 10 having essentially equal contents of Mg and Si but different amounts of the elements Mn, Cr, V, Cu and Ti.
  • the alloy X1 is the base alloy, meaning that the other alloys consist of alloy X1 with additional alloying elements.
  • the Mg and Si contents are slightly higher than those of the alloys of Table 9, which means that the strength after age hardening of the alloys of Table 10 in general is slightly higher than the strength after age hardening of the alloys of Table 9.
  • Table 10 Composition of the alloys of Example 8.
  • Fig. 19 indicates that among the tested alloy compositions, the addition of Mn+Cr has the highest positive influence on the Charpy energy whereas the additions of Mn+V and Mn+Ti have the second highest positive influence on the Charpy energy.

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  • Chemical & Material Sciences (AREA)
  • Engineering & Computer Science (AREA)
  • Materials Engineering (AREA)
  • Mechanical Engineering (AREA)
  • Metallurgy (AREA)
  • Organic Chemistry (AREA)
  • Physics & Mathematics (AREA)
  • Thermal Sciences (AREA)
  • Crystallography & Structural Chemistry (AREA)
  • Extrusion Of Metal (AREA)
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Abstract

L'invention concerne un alliage Al-Mg-Si présentant une ductilité et des propriétés d'écrasement améliorées, ledit alliage étant notamment utile pour des composants structuraux dans les zones exposées à l'écrasement dans des véhicules. L'alliage contient en % en poids : Mg 0,25 - 1,2 ; Si 0,3 - 1,4 ; Ti 0,03 - 0,4, Ti étant présent en solution solide et l'alliage contenant en plus un ou plusieurs des composants d'alliage suivants : Mn max 0,6 ; Cr max 0,3 ; Zr max 0,25, et des impuretés accidentelles, y compris Fe et Zn jusqu'à 0,5, le reste étant Al.
EP07715944A 2006-02-17 2007-02-16 Alliage en aluminium presentant des proprietes d'ecrasement ameliorees Withdrawn EP1987170A1 (fr)

Applications Claiming Priority (2)

Application Number Priority Date Filing Date Title
NO20060794 2006-02-17
PCT/NO2007/000057 WO2007094686A1 (fr) 2006-02-17 2007-02-16 Alliage en aluminium presentant des proprietes d'ecrasement ameliorees

Publications (1)

Publication Number Publication Date
EP1987170A1 true EP1987170A1 (fr) 2008-11-05

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EP07715944A Withdrawn EP1987170A1 (fr) 2006-02-17 2007-02-16 Alliage en aluminium presentant des proprietes d'ecrasement ameliorees

Country Status (5)

Country Link
US (1) US20090116999A1 (fr)
EP (1) EP1987170A1 (fr)
JP (1) JP2009526913A (fr)
CN (1) CN101384741A (fr)
WO (1) WO2007094686A1 (fr)

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EP2728026A1 (fr) 2010-04-26 2014-05-07 Sapa AB Matériau d'aluminium tolérant les dommages présentant une microstructure lamellaire

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JP5599588B2 (ja) * 2009-09-24 2014-10-01 株式会社神戸製鋼所 電池ケース用アルミニウム合金板およびその製造方法ならびに電池ケース
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CA2817425C (fr) * 2012-05-31 2020-07-21 Rio Tinto Alcan International Limited Alliage d'aluminium combinant une resistance, une elongation et une extrudabilite elevees
US9890443B2 (en) * 2012-07-16 2018-02-13 Arconic Inc. 6XXX aluminum alloys, and methods for producing the same
JP6022882B2 (ja) * 2012-10-05 2016-11-09 株式会社Uacj 高強度アルミニウム合金押出材及びその製造方法
CA2912021C (fr) * 2013-06-19 2020-05-05 Rio Tinto Alcan International Limited Composition d'alliage d'aluminium presentant des proprietes mecaniques ameliorees, a temperature elevee
CA2931354A1 (fr) * 2013-11-27 2015-06-04 Rio Tinto Alcan International Limited Alliage d'aluminium combinant de hautes resistance et aptitude a l'extrusion et une faible sensibilite a la trempe
KR102437942B1 (ko) 2014-01-21 2022-08-29 아르코닉 테크놀로지스 엘엘씨 6xxx 알루미늄 합금
CN104789831B (zh) * 2014-05-30 2018-08-31 安徽鑫发铝业有限公司 一种时效强化铝合金型材
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CN104988366A (zh) * 2015-07-07 2015-10-21 龙口市丛林铝材有限公司 一种轨道车辆车体用吸能铝型材及其制备方法
CN105220036A (zh) * 2015-10-22 2016-01-06 浙江科隆五金股份有限公司 新型铝合金构件
CN105483464B (zh) * 2015-12-17 2017-09-22 上海友升铝业有限公司 一种适用于汽车保险杠吸能盒的Al‑Mg‑Si系合金材料
JP6727310B2 (ja) 2016-01-08 2020-07-22 アーコニック テクノロジーズ エルエルシーＡｒｃｏｎｉｃ Ｔｅｃｈｎｏｌｏｇｉｅｓ Ｌｌｃ 新６ｘｘｘアルミニウム合金及びその製造方法
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WO2007094686A8 (fr) 2008-09-25
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US20090116999A1 (en) 2009-05-07
WO2007094686A1 (fr) 2007-08-23

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