Patent Application
20140224859
The present invention relates to a friction stir welding tool and a method for manufacturing the same.
In 1991, a friction stir welding technique of joining metal materials such as aluminum alloys together was established in the United Kingdom. This technique joins metal materials to each other in the following way. A cylindrical friction stir welding tool having a small-diameter protrusion formed at a tip thereof is pressed against joint surfaces of the metal materials to be joined. Meanwhile, the friction stir welding tool is rotated to thereby generate frictional heat. This frictional heat causes the metal materials of the joint portion to soften and plastically flow, and thereby joins the metal materials together.
“Joint portion” herein refers to a joint interface portion where joining of metal materials by butting the metal materials or placing one metal material on top of the other metal material is desired. Near this joint interface, the metal materials are caused to soften and plastically flow, and the metal materials are stirred. As a result, the joint interface disappears and the metal materials are joined. Simultaneously with the joining, dynamic recrystallization occurs to the metal materials. Due to this dynamic recrystallization, the metal materials near the joint interface become fine particles, and thus the metal materials can be joined with a high strength (Japanese Patent Laying-Open No. 2003-326372 (PTD 1)).
When aluminum alloys are used as the above-mentioned metal materials, plastic flow occurs at a relatively low temperature of approximately 500° C. Therefore, even when the friction stir welding tool made of an inexpensive tool steel is used, little wear and tear occurs and frequent replacement of the friction stir welding tool is unnecessary. Therefore, for the friction stir welding technique, the cost required to join the aluminum alloys is low. Thus, in place of a resistance welding method for melting and joining aluminum alloys, the friction stir welding technique has already been in practical use in various applications as a technique of joining parts of a railroad vehicle, a motor vehicle or an aircraft.
In order to improve the life of the friction stir welding tool, it is necessary to improve the wear resistance and the adhesion resistance of the friction stir welding tool. Friction stir welding uses frictional heat, which is generated by friction between the friction stir welding tool and the workpieces to be joined, to cause the workpieces to soften and plastically flow, and thereby join the workpieces together. Thus, in order to increase the joining strength to join the workpieces together, it is necessary to efficiently generate the frictional heat.
PTD 1, Japanese Patent Laying-Open No. 2005-199281 (PTD 2), and Japanese Patent Laying-Open No. 2005-152909 (PTD 3) each disclose an attempt to improve the tool life through improvements of the wear resistance and the adhesion resistance of the friction stir welding tool.
For example, a friction stir welding tool of PTD 1 has a diamond film coating on the surface of a base material formed of a cemented carbide or silicon nitride. Since the diamond film is excellent in hardness and wear resistance and has a low friction coefficient, workpieces are less likely to be adhered to the friction stir welding tool. Accordingly, the workpieces can successfully be joined together.
In contrast, according to PTD 2, a probe pin and a rotator, which constitute a part of the surface of a friction stir welding tool and are to be brought into contact with workpieces, are formed of a cemented carbide containing 5 to 18% by mass of Co. Because of such a content of Co, the affinity of the friction stir welding tool for the workpieces is low and the workpieces are less likely to adhere to the tool. Moreover, since a cemented carbide having a thermal conductivity of 60 W/m·K or more is used for the base material, heat is likely to be released and diffused into the outside, and buckling of the rotator and the probe pin as well as thermal deformation of the joint of the workpieces hardly occur.
According to PTD 3, a friction stir welding tool has an anti-adhesion layer that is made of any of diamond-like carbon, TiN, CrN, TiC, SiC, TiAlN, and AlCrSiN and coats the surface of a portion of the tool that is to be brought into contact with workpieces. According to PTD 3, the tool also has an underlying layer made of any of TiN, CrN, TiC, SiC, TiAlN, and AlCrSiN and provided between a base material and the anti-adhesion layer to coat the base material. The underlying layer can thus be provided to enhance the adherence between the base material and the anti-adhesion layer, make the anti-adhesion layer less likely to crack, and improve the wear resistance. Moreover, diamond-like carbon to be used for the anti-adhesion layer has a low affinity for soft metals such as aluminum and is thus excellent in adhesion resistance.
The diamond film of PTD 1 inherently has a large surface roughness. If the thickness of the diamond film is increased in order to enhance the wear resistance, the surface roughness is made still larger with the increase of the thickness of the diamond film. A resultant disadvantage is a considerably low adhesion resistance unless the surface of the diamond film is polished after the coating with the diamond film.
In addition, due to a very high thermal conductivity of the diamond film, frictional heat generated by friction between the tool and the workpieces is likely to escape into the outside, which makes it difficult to increase the temperature of the tool in an initial stage after the start of joining. Therefore, in the initial stage of joining, the workpieces are hindered from plastically flowing, and a stable joining strength fails to be achieved. Moreover, the diamond film involves a problem that, because the growth speed of the diamond film is slow, the manufacturing cost is accordingly high.
While the friction stir welding tool of PTD 2 has an advantage that the high content of Co makes the tool less likely to break, the tool is insufficient in terms of the adhesion resistance when used to join soft metals such as aluminum. Moreover, because PTD 2 uses a cemented carbide having a high thermal conductivity, the frictional heat escapes in the initial stage after the start of joining and thus a stable joining strength cannot be achieved.
As for PTD 3, diamond-like carbon used for the anti-adhesion layer has a very small friction coefficient and therefore frictional heat is difficult to be generated by friction between the tool and the workpieces. A resultant problem is therefore that the probe cannot be inserted in the workpieces or, even if the probe can be inserted in the workpieces, a long time is required for completion of joining. Moreover, a nitride-based anti-adhesion layer that is used as the anti-adhesion layer of PTD 3 is inadequate in terms of adhesion resistance to soft metals such as aluminum.
As seen from the foregoing, the friction stir welding tools of PTD 1 to PTD 3 all fail to successfully achieve both the stability of joining in the initial stage of joining and the adhesion resistance, and are required to have further improved wear resistance and chipping resistance.
The present invention has been made in view of the present circumstances as described above, and an object of the invention is to provide a friction stir welding tool that exhibits excellent adhesion resistance even when used to join soft metals, as well as excellent wear resistance, and provides a stable joining strength and a stable joining quality all along from the initial stage after the start of joining.
The inventors of the present invention have conducted thorough studies with the aim of improving the adhesion resistance of the friction stir welding tool to consequently find that a coating layer containing cubic WC1-x can be formed on a surface of a base material to thereby improve the adhesion resistance without reducing frictional heat. They have further found that the thermal conductivity, the WC particle size, and the Co content of a cemented carbide of which the base material is made can be optimized to provide excellent adhesion resistance even when soft metals are joined, as well as excellent wear resistance and chipping resistance, and accordingly a stable joining quality all along from the initial stage after the start of joining.
More specifically, a friction stir welding tool of the present invention is used for friction stir welding, and includes: a base material; and a coating layer formed on a surface of at least a portion of the base material that is to be caused to contact workpieces during friction stir welding, the base material being formed of a cemented carbide, and the coating layer containing cubic WC1-x.
The coating layer is formed by electrical discharge machining. The base material is preferably formed of a cemented carbide having a thermal conductivity of less than 60 W/m·K. The base material preferably contains WC having an average particle size of not less than 0.1 μm and not more than 1 μm, and preferably contains not less than 3% by mass and not more than 15% by mass of Co.
The coating layer subjected to x-ray diffraction preferably has I (WC1-x)/I (W2C) of not less than 2, where I (WC1-x) is a higher one of respective diffracted beam intensities of (111) diffracted beam and (200) diffracted beam, and I (W2C) is a highest one of respective diffracted beam intensities of (1000) diffracted beam, (0002) diffracted beam, and (1001) diffracted beam.
The coating layer preferably has a surface roughness Ra of not less than 0.05 μm and not more than 0.6 μm.
Friction stir welding by means of the friction stir welding tool is preferably spot joining.
The present invention also provides a method for manufacturing a friction stir welding tool, including the step of performing electrical discharge machining on a base material formed of a cemented carbide to simultaneously process the base material and form a coating layer on a surface of at least a portion of the base material that is to be caused to contact workpieces, the coating layer containing cubic WC1-x.
The friction stir welding tool of the present invention has the above-described configuration, and therefore exhibits superior effects that the tool has excellent adhesion resistance even when used to join soft metals, as well as excellent wear resistance and chipping resistance, and provides a stable joining quality all along from the initial stage after the start of joining.
The present invention will be described in more detail hereinafter.
<Friction Stir Welding Tool>
As shown in
Preferably, the friction stir welding tool of the present invention has a helical screw thread portion 8 formed on the side of probe portion 4 as shown in
<Base Material>
Base material 2 in the friction stir welding tool of the present invention is characterized by its containing a cemented carbide (e.g., WC-based cemented carbide, a material containing Co in addition to WC, or the material to which carbonitride or the like of Ti, Ta, Nb or the like is further added). The cemented carbide may contain, in its structure, free carbon or an abnormal phase called η phase. The above-identified cemented carbide has a higher hardness relative to tool steels such as SKD and SKH that are used commonly for the base material of the friction stir welding tool, and is therefore advantageous in that it has excellent wear resistance. It should be noted that WC in the cemented carbide which forms the base material has a hexagonal crystal structure.
Preferably, the base material is a cemented carbide having a thermal conductivity of less than 60 W/m·K, which is more preferably 50 W/m·K or less, and still more preferably 40 W/m·K or less. The lower limit of the thermal conductivity is preferably 20 W/m·K or more, and more preferably 25 W/m·K or more. A cemented carbide having such a thermal conductivity can be used for the base material to make it less likely that frictional heat generated by friction escapes and accordingly facilitate raising the temperature of the workpieces, even when the rotational speed of the friction stir welding tool is low and the load for joining is small. Thus, the probe portion can be inserted into the workpieces in a short period of time, and accordingly the time taken for spot joining can be shortened. Particularly in the case of spot joining, the temperature of the friction stir welding tool sharply increases from the initial stage after the start of joining. In this case as well, stable joining strength can be achieved all along from the initial stage after the start of joining. A thermal conductivity of the cemented carbide of 60 W/m·K or more is not preferred, because the frictional heat generated by friction between the friction stir welding tool and the workpieces escapes, which hinders the temperature of the tool and the workpieces from increasing. In addition, because of the composition of the cemented carbide, a base material having a thermal conductivity of less than 20 W/m·K is difficult to produce. As “thermal conductivity” herein, a value is used that has been calculated based on the thermal diffusivity of the base material measured in accordance with the laser flash method as well as the specific heat and the density of the base material.
WC contained in the base material preferably has an average particle size of not less than 0.1 μm and not more than 1 μm. If the average particle size of WC is less than 0.1 μm, it is industrially difficult to prepare the cemented carbide. On the contrary, if it is more than 1 μm, the thermal conductivity may be 60 W/m·K or more depending on the case, which is therefore not preferred. Namely, in order for the cemented carbide to have a thermal conductivity of less than 60 W/m·K, it is necessary that the average particle size of WC be 1 μm or less. In the case where the screw thread is formed on the probe portion, WC having an average particle size of 1 μm or less makes it less likely that the apex of the screw thread is chipped, and thereby improves the life of the friction stir welding tool. The average particle size of WC is more preferably 0.2 μm or more and 0.7 μm or less. An average particle size of WC of 0.7 μm or less makes the thermal conductivity of the base material still smaller, and therefore makes it still less likely that frictional heat escapes. Thus, the life of the friction stir welding tool can be improved, the time taken for joining can also be shortened, and the strength of joining is stable all along from the initial stage after the start of joining. On the contrary, an average particle size of WC of 0.2 μm or more has an advantage that preparation of the cemented carbide in an industrial production process is facilitated.
As the above-indicated average particle size of the WC particles, the value of measurement taken in the following way is used. First, a scanning electron microscope (SEM) and an associated wavelength dispersive x-ray analysis (EPMA: Electron Probe Micro-Analysis) are used to map WC particles and other components in a base material's cross section (a plane perpendicular to the direction of the leading end of the probe portion). Next, the number of WC particles that are present on an arbitrary line of 20 μm in the cross section is counted, and the total length of regions occupied by the WC particles respectively on that line is measured. Subsequently, the total length thus measured is divided by the number of the WC particles and the determined value of the quotient is the particle size of the WC particles. For three arbitrary lines, measurements are taken in a similar manner to determine respective particle sizes of individual WC particles, and the average of them is determined for use as the average particle size of the WC particles.
The cemented carbide forming the base material preferably contains not less than 3% by mass and not more than 15% by mass of Co, more preferably contains not less than 6% by mass and not more than 12% by mass of Co, and still more preferably contains not less than 8% by mass and not more than 10% by mass of Co. A Co content of more than 15% by mass is not preferred because it causes deterioration of the wear resistance. A Co content of less than 3% by mass is not preferred because it causes deterioration of the breakage resistance, which may result in chipping of the screw thread of the probe portion and, in the case of linear joining, may result in breakage of the probe portion.
The Co content in the cemented carbide is herein a value determined in the following way. The friction stir welding tool is mirror-polished, the crystal structure forming an arbitrary region of the base material is photographed at a magnification of 10000× by the SEM, the associated EPMA is used to map the Co component in a base material's cross section (a plane perpendicular to the direction of the leading end of the probe portion), and the total area of Co in the photograph is converted into the mass ratio, which is used as the Co content.
<Coating Layer>
In the friction stir welding tool of the present invention, coating layer 3 is characterized by being formed, as shown in
The coating layer is characterized by its containing cubic WC1-x. Cubic WC1-x is superior to nitrides such as TiN and CrN as well as TiC and SiC in terms of adhesion resistance, and therefore, soft metals such as aluminum are less likely to adhere thereto. In addition, the friction coefficient of cubic WC1-x is not as low as the friction coefficient of diamond-like carbon (DLC). Therefore, regarding the friction stir welding tool including the coating layer made of cubic WC1-x, generation of the friction heat by friction with workpieces is facilitated. Moreover, cubic WC1-x has an advantage that it has a high hardness and is therefore superior in wear resistance. WC in the cemented carbide of the tool's base material has a hexagonal crystal structure. In contrast, cubic WC1-x has a cubic NaCl type crystal structure. Here, 1-x of WC1-x means that C is less than 1 in the stoichiometric composition of WC. In accordance with a W-C binary equilibrium diagram, cubic WC1-x is present in a limited region, and x of WC1-x is said to be 0.3 to 0.4 at 2380±30° C. to 2747±12° C.
According to the present invention, while the coating layer may contain W2C as another tungsten carbide other than cubic WC1-x, it is preferable that W2C is not contained as far as possible because the hardness of W2C is low. Here, the crystal structure of the tungsten carbide contained in the coating layer can be confirmed through x-ray diffraction. Diffracted beams of cubic WC1-x correspond to those in JCPDS card 20-1316.
The coating layer subjected to x-ray diffraction has I (WC1-x)/I (W2C) of preferably not less than 2, where I (WC1-x) is a higher one of respective diffracted beam intensities of (111) diffracted beam and (200) diffracted beam, and I (W2C) is a highest one of respective diffracted beam intensities of (1000) diffracted beam, (0002) diffracted beam, and (1001) diffracted beam. This ratio is more preferably 5 or more, and still more preferably 10 or more. The coating layer can contain cubic WC1-x at this ratio to thereby have a higher hardness, so that the wear resistance and the chipping resistance of the friction stir welding tool can be improved.
The coating layer of the present invention preferably has a thickness of not less than 1 μm and not more than 20 μm. This thickness of 1 μm or more enables the wear resistance to be improved and the tool life to remarkably be extended. The coating layer of the present invention has a thickness of more preferably not less than 2 μm and not more than 15 μm, and still more preferably not less than 3 μm and not more than 10 μm. Accordingly, the tool life can further be extended, and the chipping resistance can be made higher.
It should be noted that the thickness of the coating layer of the present invention is herein the thickness of the coating layer of any portion of the surface of the friction stir welding tool, and is for example the thickness of the coating layer at the leading end of the probe, of the thickness of the whole coating layer formed on the base material of the friction stir welding tool.
The coating layer of the present invention preferably has a surface roughness, which is an arithmetic mean roughness Ra (hereinafter also referred to simply as “surface roughness Ra”) defined by JIS B0601, of not less than 0.05 μm and not more than 0.6 μm. A surface roughness Ra of less than 0.05 μm may not be preferred, because such a surface roughness hinders heat from being generated by friction between the tool surface and the workpieces during joining, and accordingly hinders the probe pin from being inserted, resulting in a longer time to be taken for spot joining. A surface roughness Ra of more than 0.6 μm makes it more likely that the workpieces adhere to the tool surface, which therefore may not be preferred. A more preferred range of surface roughness Ra is not less than 0.1 μm and not more than 0.5 μm.
The surface roughness of the coating layer can be changed by the conditions for electrical discharge machining. The conditions for electrical discharge machining, which may chiefly be discharge time, pause time, and current peak value, can appropriately be adjusted to thereby adjust the surface roughness of the coating layer. A slower machining rate makes the surface roughness smaller, and a higher machining rate makes the surface roughness larger.
The coating layer of the present invention may be formed to cover the whole surface of the base material, or a part of the base material may not be covered with the coating layer, or the structure of the coating layer may be different depending on the location on the base material, which, however, does not go beyond the scope of the present invention.
<Method for Forming Coating Layer>
According to the present invention, the coating layer may be formed by electrical discharge machining performed on the surface of the base material. Electrical discharge machining can not only process the shape of the base material but also form the coating layer containing cubic WC1-x on the surface of the base material, and thus has advantages that the friction stir welding tool can conveniently be fabricated and the manufacturing cost can be reduced.
While any known technique may be used for the above-described electrical discharge machining, the electrical discharge machining is more preferably die-sinker electrical discharge machining using an electrode of copper, copper tungsten, silver tungsten, graphite, or the like. Die-sinker electrical discharge machining is more preferred since it can form a coating layer having a higher content of cubic WC1-x and accordingly enhance the wear resistance, as compared with wire-cut electrical discharge machining using a brass wire. In particular, for die-sinker electrical discharge machining, an electrical discharge condition that the machining rate is 0.005 to 0.05 g/min can be selected to increase the content of cubic WC1-x.
As seen from the foregoing, the method for manufacturing a friction stir welding tool according to the present invention includes the step of performing electrical discharge machining on a base material formed of a cemented carbide to simultaneously process the base material and form a coating layer on a surface of at least a portion of the base material that is to be caused to contact workpieces, and the coating layer contains cubic WC1-x.
In the following, the present invention will be described in more detail with reference to Examples. The present invention, however, is not limited to them. It should be noted that the thickness of the coating layer in the Examples was measured by directly observing a cross section of the coating layer by means of a scanning electron microscope (SEM).
For Examples 1 to 14 each, a friction stir welding tool as shown in
The friction stir welding tools for the Examples and Comparative Examples each had probe portion 4 and shoulder portion 6 as shown in
The leading end of cylindrical portion 5, shoulder portion 6, and probe portion 4 in
For Comparative Examples 1 to 2 each, a friction stir welding tool was fabricated in a similar way to Example 1, except that a cemented carbide having characteristics shown in Table 1 below was used for the base material, and the base material was entirely subjected to grinding without the coating layer formed thereon.
For Comparative Example 3, a cemented carbide having characteristics shown in Table 1 below was used for the base material and, on the surface of a friction stir welding tool entirely subjected to grinding like Comparative Example 1, a TiN coating layer was formed by means of the vacuum arc vapor deposition method. The coating layer was formed by a vacuum arc vapor deposition method through the following procedure.
First, the base material was set on a base material holder in a chamber of a vacuum arc vapor deposition apparatus, and Ti was set as a target of a metal evaporation source. Then, vacuum was generated and cleaning was performed. Next, nitrogen gas was introduced, the pressure in the chamber was set to 3.0 Pa, and the voltage of a DC bias power source for the base material was set to −50 V. Subsequently, the above Ti target was ionized with arc current 200 A, to thereby cause Ti and N2 gas to react with each other. Thus, the TiN coating layer was formed on the base material.
For Comparative Example 4, a CrN coating layer was formed on the base material in a similar manner to Comparative Example 3, except that Ti of Comparative Example 3 was replaced with Cr.
For Comparative Example 5, a friction stir welding tool was fabricated in a similar way to Comparative Example 3, except that a coating layer made of diamond-like carbon (DLC) was formed by means of a plasma CVD method. The coating layer was formed by the plasma CVD method through the following procedure.
First, the base material was set on a base material holder in a chamber of a plasma CVD apparatus. Then, a vacuum pump was used to reduce the pressure in the chamber, a heater installed in the apparatus was used to heat the base material to a temperature of 200° C., and the chamber was evacuated until the pressure in the chamber reached 1.0×10−3 Pa.
Next, argon gas was introduced, the pressure in the chamber was kept at 3.0 Pa, and high-frequency power 500 W was applied to the base material holder, to clean the surface of the base material for 60 minutes. After this, the chamber was evacuated, and thereafter CH4 was introduced so that the pressure in the chamber was 10 Pa. Next, high-frequency power 400 W was applied to the base material holder to form a coating layer made of DLC.
The value of “thermal conductivity” in Table 1 was calculated based on the thermal diffusivity of the base material measured by means of the laser flash method, as well as the specific heat and the density of the base material. The value of the thermal diffusivity was obtained by using a laser flash apparatus (xenon flash analyzer LFA447 (manufactured by NETZSCH)) to measure a sample having a size of 08 mm×thickness 1.5 mm.
The friction stir welding tools of the Examples and Comparative Examples thus obtained were each mirror-polished, and the base material in an arbitrary region was photographed at a magnification of 10000× by an SEM, and an associated EPMA was used to map the Co component in a base material's cross section (a plane perpendicular to the direction of the leading end of the probe portion). Then, for the 10000× photograph thus taken, image processing software was used to calculate the total area of Co and meanwhile, the components were identified. The Co ratio to the base material in the photograph was converted into the mass ratio by percentage, to thereby calculate the mass percentage of Co in the base material. The results are shown under “Co content” in Table 1.
Further, the number of WC particles on an arbitrary line of 20 μm in the cross section of the base material was counted, and the total length of regions occupied by the WC particles respectively on that line was measured. The total length thus measured was divided by the number of the WC particles and the determined value of the quotient was the particle size of the WC particles. For three arbitrary lines, measurements were taken in a similar manner to determine respective particle sizes of individual WC particles. The results are shown under “WC average particle size” in Table 1.
The coating layer formed for each Example was analyzed based on XRD (x-ray diffraction), observation of a cross section with an SEM, and EPMA. The results are shown in the column under “crystal structure/composition” in Table 1. It should be noted that, regarding “cubic WC1-x” in Table 1, the value of x is not specified since the coating layer also contains W2C and the ratio therebetween is difficult to quantify. As clearly seen from Table 1, it has been confirmed that the friction stir welding tool of each Example has the coating layer made of cubic WC1-x and W2C. In contrast, on the surface of the friction stir welding tool of Comparative Examples 1 to 2 each, the coating layer containing cubic WC1-x was not present, and a cemented carbide made of the same hexagonal WC and Co as those in the base material was identified.
Furthermore, the peak intensity ratio I (WC1-x)/I(W2C) between cubic WC1-x and W2C forming the coating layer was calculated based on XRD (x-ray diffraction). Here, I (WC1-x) is a higher one of respective diffracted beam intensities of (111) diffracted beam and (200) diffracted beam, and I (W2C) is a highest one of respective diffracted beam intensities of (1000) diffracted beam, (0002) diffracted beam, and (1001) diffracted beam. The results are shown in the column under “I (WC1-x)/I (W2C)” in Table 1.
<Evaluation of Friction Stir Welding Tool (Spot Joining Test)>
Each of the friction stir welding tools of the Examples and Comparative Examples thus fabricated was used to conduct a spot joining test by doing 100,000 strokes of spot joining. Workpieces were two sheets of aluminum alloy A5052 each having a thickness of 1 mm. These workpieces were laid on each other and the test was performed under friction stir welding conditions that the tool load was 400 kgf, the tool rotational speed was 3000 rpm, and the time for joining was 2.0 seconds. Based on this, the adhesion resistance, the wear resistance, the chipping resistance, and the stability of the joining strength in an initial stage after the start of joining were evaluated. In the case where adhesion of the workpieces was confirmed before performing 100,000 strokes of spot joining, the spot joining test was stopped at this time. The following is a description of how the above items were each evaluated. The following evaluation results are each shown in the column under “spot joining evaluation” in Table 2.
Evaluation of Adhesion Resistance
The adhesion resistance was evaluated in the following manner. Each time 5,000 strokes of spot joining were done, the friction stir welding tool was removed and a microscope was used to confirm whether the workpieces had adhered to the tool. The time when adhesion of the workpieces was confirmed is indicated in the column under “state of occurrence of adhesion” in Table 2. In the case where adhesion of the workpieces was not confirmed even after 100,000 strokes of spot joining, this was evaluated as “no adhesion.” In the case of occurrence of adhesion, a greater number of strokes of the spot joining in the column “state of occurrence of adhesion” represents a higher adhesion resistance.
Evaluation of Wear Resistance
The wear resistance was evaluated based on the decrease of the diameter of the probe portion at the time when 100,000 strokes of spot joining were completed. The diameter of the probe portion after 100,000 strokes of spot joining was measured with a vernier caliper to thereby calculate the amount of wear of the probe portion. The results are shown in the column under “variation of probe diameter” in Table 2. A smaller variation of the probe diameter means that the tool is less likely to wear and has higher wear resistance. Regarding Comparative Examples 1 to 5, adhesion of the workpieces was confirmed before 100,000 strokes of spot joining, and therefore, evaluation of the wear resistance was not done.
Evaluation of Chipping Resistance
The chipping resistance was evaluated in the following manner. After 100,000 strokes of spot joining, a microscope was used to observe the probe portion and the screw thread portion to confirm the state of fracture of the probe portion and the screw thread portion. Regarding Comparative Examples 1 to 5, adhesion of the workpieces was confirmed before 100,000 strokes of spot joining, and therefore, evaluation of the chipping resistance was not done. The results are shown in the column under “state of fracture” in Table 2.
Evaluation of Stability of Joining Strength
The stability of the joining strength in an initial stage after the start of joining was evaluated in the following manner. A micrometer was used to measure the remaining thickness of the lower one of spot-joined workpieces. The number of strokes of spot joining required to be done for the remaining thickness of the lower workpiece to become 0.5 mm or less was used for evaluation. More specifically, in the present spot joining test, it was determined that the joining strength was stable when the remaining thickness of the lower workpiece was 0.5 mm or less, since the total thickness of the workpieces was 2 mm and the length of the friction stir welding tool from the surface of the shoulder portion to the leading end of the probe portion was 1.5 mm, and thus the probe portion was completely inserted in the workpieces when the remaining thickness was 0.5 mm or less. A smaller number of strokes of spot joining required to be done for the remaining thickness to become 0.5 mm or less means that the joining strength was more stable all along from the initial stage after the start of joining.
<Evaluation of Friction Stir Welding Tool (Linear Joining Test)>
Each of the friction stir welding tools of the Examples and Comparative Examples thus fabricated was used to perform linear butt-joining on workpieces, specifically sheets of aluminum alloy A6061 of 2 mm in thickness, under the friction stir welding conditions that the tool rotational speed was 2000 rpm and the joining rate was 1000 mm/min, until a joint of 1000 m was formed. Based on this, the adhesion resistance, the wear resistance, and the chipping resistance were evaluated. In the case where adhesion of the workpieces was confirmed before the joint of 1000 m was formed, the linear joining test was stopped at this time. The following evaluation results are shown in the columns under “linear joining evaluation” in Table 2.
Evaluation of Adhesion Resistance
The adhesion resistance was evaluated in the following manner. Each time a linear joint of 100 m was formed, the friction stir welding tool was removed and a microscope was used to confirm whether the workpieces had adhered to the tool. The time when adhesion of the workpieces was confirmed is indicated in the column under “state of occurrence of adhesion” in Table 2. In the case where adhesion of the workpieces was not confirmed even after a linear joint of 1000 m was formed, this was evaluated as “no adhesion.” A greater numerical value of the length of the joint in the column “state of occurrence of adhesion” represents a higher adhesion resistance.
Evaluation of Wear Resistance
The wear resistance was evaluated based on the decrease of the diameter of the probe portion at the time when a linear joint of 1000 m was completed. The diameter of the probe portion after the linear joint of 1000 m was formed was measured with a vernier caliper to thereby calculate the amount of wear of the probe portion. The results are shown in the column under “variation of probe diameter” in Table 2. A smaller variation of the probe diameter means that the tool is less likely to wear and has higher wear resistance. Regarding Comparative Examples 1 to 5, adhesion of the workpieces was confirmed before the linear joint of 1000 m was formed, and therefore, evaluation of the wear resistance was not done.
Evaluation of Chipping Resistance
The chipping resistance was evaluated in the following manner. After a linear joint of 1000 m was formed, a microscope was used to observe the probe portion and the screw thread portion to confirm the state of fracture of the probe portion and the screw thread portion. Regarding Comparative Examples 1 to 5, adhesion of the workpieces was confirmed before the linear joint of 1000 m was formed, and therefore, evaluation of the chipping resistance was not done. The results are shown in the column under “state of fracture” in Table 2.
<Result of Evaluation of Adhesion Resistance>
Regarding the friction stir welding tools of Examples 1 to 14, adhesion of the workpieces did not occur even after 100,000 strokes of spot joining, as shown under “state of occurrence of adhesion” under the spot joining evaluation in Table 2, and thus these tools were all excellent in adhesion resistance. Further, as shown under “state of occurrence of adhesion” under the linear joining evaluation in Table 2, adhesion of the workpieces did not occur after a linear joint of 1000 m was formed, and thus these tools were all excellent in adhesion resistance. The reason why the Examples were each excellent in adhesion resistance is considered to be the fact that, in all of the Examples, the coating layer containing cubic WC1-x was formed on the surface of the portion of the base material that was caused to contact the workpieces.
In contrast, regarding Comparative Examples 1 to 5, adhesion of the workpieces occurred before 100,000 strokes of spot joining were done or a linear joint of 1000 m was formed, as shown under “state of occurrence of adhesion” in Table 2. The reason why the adhesion resistance of Comparative Examples 1 and 2 was thus low is considered to be the fact that the coating layer was not formed. As to Comparative Examples 3 to 5 as well, the fact that the coating layer did not contain cubic WC1-x is considered to be a reason for adhesion of the workpieces.
<Result of Evaluation of Wear Resistance>
As shown under “variation of probe diameter” under the spot joining evaluation in Table 2, all of the Examples except for Example 8 had a variation of the probe diameter of 0.01 mm or less after 100,000 strokes of spot joining, and were thus excellent in wear resistance. Further, as shown under “variation of probe diameter” under the linear joining evaluation in Table 2, all of the Examples except for Example 8 had a variation of the probe diameter of 0.01 mm or less after a linear joint of 1000 m was formed, and were thus excellent in wear resistance. The reason why these Examples had excellent wear resistance is considered to be the fact that the content of Co contained in the base material was 15% by mass or less in all of the Examples except for Example 8. In contrast, as to Example 8, the fact that the Co content exceeded 15% by mass (17% by mass) is considered to be a reason for the lower wear resistance and the variation of the probe diameter exceeding 0.01 mm.
<Result of Evaluation of Chipping Resistance>
As shown under “state of fracture” under the spot joining evaluation in Table 2, all of the Examples except for Example 3 had no damage to the probe portion and the screw thread portion even after 100,000 strokes of spot joining, and were thus excellent in chipping resistance. As shown under “state of fracture” under the linear joining evaluation in Table 2, all of the Examples except for Example 3 had no damage to the probe portion and the screw thread portion even after a linear joint of 1000 m was formed, and were thus excellent in chipping resistance. The reason why these Examples had excellent chipping resistance is considered to be the fact that the content of Co contained in the base material was 3% by mass or more in all of the Examples except for Example 3. In contrast, as to Example 3, the fact that the Co content was less than 3% by mass (2% by mass) is considered to be a reason for the lower chipping resistance and occurrence of chipping to the probe portion or the screw thread portion. Specifically, in Example 3, a part of the screw thread portion had been lost at the time after 100,000 strokes of spot joining were done. Further, in Example 3, a part of the screw thread portion had been lost at the time after a linear joint of 1000 m was formed.
As seen from the results indicated under “number of strokes for remaining thickness of lower workpiece to become 0.5 mm” in Table 2, all of the Examples except for Examples 9 and 11 to 14 had a remaining thickness of the lower workpiece of 0.5 mm or less at the time when the first stroke of spot joining was done, which means that joining could be performed with a stably high joining strength all along from the initial stage of joining. The reason for this is considered to be the fact that all of the Examples except for Examples 9 and 11 to 14 used a base material including a cemented carbide having a thermal conductivity of less than 60 W/m·K, and therefore, increase of the tool temperature was facilitated. In contrast, Examples 9 and 11 to 14 used a base material including a cemented carbide having a thermal conductivity of 60 W/m·K or more, and therefore, increase of the tool temperature was hindered and the remaining thickness of the lower workpiece was more than 0.5 mm when the first/second stroke of spot joining was done.
In contrast, regarding the friction stir welding tool of Comparative Example 5, the coefficient of friction between the workpieces and diamond-like carbon forming the coating layer was low, which hindered generation of the frictional heat and accordingly the remaining thickness of the lower workpiece became 0.5 mm or less at the time when the eighth stroke of spot joining was done. As seen from the above, the coating layer made of diamond-like carbon results in a low joining stability in the initial stage after the start of joining.
From the foregoing results, it has been confirmed that the friction stir welding tools of Examples 1 to 14 according to the present invention are superior in adhesion resistance, wear resistance, and chipping resistance as compared with the friction stir welding tools of Comparative Examples 1 to 5, and achieve stable joining all along from the initial stage after the start of joining.
The conditions for electrical discharge machining were changed to fabricate friction stir welding tools that were different in surface roughness Ra of the coating layer. Except that the conditions for electrical discharge machining were changed, the same fabrication method as Example 5 was used (conditions for electrical discharge machining were adjusted in such a manner that the discharge time, the pause time, and the current peak value were adjusted so that the machining rate was 0.005 to 0.01 g/min).
On these tools, the spot joining test and the linear joining test were conducted in a similar manner to Examples 1 to 14. The results are shown in Table 3 (the results of the spot joining test are indicated under “spot joining evaluation” and the results of the linear joining test are indicated under “linear joining evaluation”). Table 3 also indicates the results for Example 5. As for Examples 20 and 21, evaluation was stopped at the time when adhesion occurred, and the variation of the prove diameter was measured after removal of adhered workpiece.
The friction stir welding tools of Examples 5 and 15 to 21 according to the present invention all exhibited excellent adhesion resistance, wear resistance, and chipping resistance as a result of both the spot joining test and the linear joining test. The friction stir welding tool of Example 19 was also superior, like the other Examples, in terms of the values of adhesion resistance, wear resistance, and chipping resistance. As to Example 19, however, due to a smaller surface roughness Ra of 0.03 μm, five strokes of spot joining were required for the remaining thickness of the lower workpiece to become 0.5 mm. As to the friction stir welding tools of Examples 20 and 21, because they had a larger surface roughness Ra of 0.64 μm and 1.2 μm respectively, the number of strokes of spot joining and the length of joint at the time adhesion occurred were smaller than other Examples. It is understood from these results that particularly excellent effects are exhibited when the surface roughness Ra is set to not less than 0.05 μm and not more than 0.6 μm.
While the embodiments and examples of the present invention have been described above, it is also originally intended to combine characteristics of the above-described embodiments and examples as appropriate.
It should be understood that the embodiments and examples disclosed herein are illustrative and not limitative in any respect. The scope of the present invention is defined by the terms of the claims, rather than the description above, and is intended to include any modifications within the scope and meaning equivalent to the terms of the claims.
| Number | Date | Country | Kind |
|---|---|---|---|
| 2012-043982 | Feb 2012 | JP | national |
| Filing Document | Filing Date | Country | Kind | 371c Date |
|---|---|---|---|---|
| PCT/JP2013/054783 | 2/25/2013 | WO | 00 | 12/12/2013 |
