Nanoscale precipitates strengthened lanthanum-bearing Mg-3Sn-1Mn alloys through continuous rheo-rolling

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T10377 Metal and Thin Film Mechanics

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Abstract We elucidate the effect of lanthanum (La) on the microstructure and mechanical properties of Mg-3Sn-1Mn- x La (wt.%) alloy plates processed through continuous rheo-rolling for the first time. At x = 0.2 wt.%, La dissolved completely in the α-Mg matrix. As the La content was increased to 0.6 wt.%, a new plate-shaped three-phase compound composed of La 5 Sn 3 , Mg 2 Sn and Mg 17 La 2 phases was formed with an average length of 380 ± 10 nm and an average width of 110 ± 5 nm. This compound had a pinning effect on the α-Mg grain boundary and on dislocations. With further increase in La-content to 1.0 wt.%, the length of the plate-shaped compound increased to an average length of 560 ± 10 nm, while the width was reduced to 90 ± 5 nm. The particle size of Mg 2 Sn decreased from 100 nm to 50 nm with increase in La-content from 0.2 to 1.4 wt.%. At La content of 1.0 wt.%, the tensile strength and elongation of the alloy was maximum, with 29% and 32% increase, respectively, compared to the Mg-3Sn-1Mn (wt.%) alloy, and 37% and 89% increase, in comparison to the Mg-3Sn-1Mn-0.87 Ce (wt.%) alloy.

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## OPEN

received: 30 November 2015

accepted: 01 March 2016

Published: 18 March 2016

# Nanoscale precipitates strengthened lanthanum-bearing Mg-3Sn-1Mn alloys through continuous rheo-rolling

R.G. Guan 1,2 , Y.F. Shen 1,2 , Z.Y. Zhao 1 & R.D.K. Misra 3

We elucidate the effect of lanthanum (La) on the microstructure and mechanical properties of Mg-
3Sn-1Mn- _x_ La (wt.%) alloy plates processed through continuous rheo-rolling for the first time. At
_x_ = 0.2 wt.%, La dissolved completely in the α-Mg matrix. As the La content was increased to 0.6 wt.%,
a new plate-shaped three-phase compound composed of La5Sn3, Mg2Sn and Mg17La2 phases was
formed with an average length of 380 ± 10 nm and an average width of 110 ± 5 nm. This compound had
a pinning effect on the α-Mg grain boundary and on dislocations. With further increase in La-content
to 1.0 wt.%, the length of the plate-shaped compound increased to an average length of 560 ± 10 nm,
while the width was reduced to 90 ± 5 nm. The particle size of Mg2Sn decreased from 100 nm to 50 nm
with increase in La-content from 0.2 to 1.4 wt.%. At La content of 1.0 wt.%, the tensile strength and
elongation of the alloy was maximum, with 29% and 32% increase, respectively, compared to the Mg-
3Sn-1Mn (wt.%) alloy, and 37% and 89% increase, in comparison to the Mg-3Sn-1Mn-0.87 Ce (wt.%)
alloy.

Magnesium (Mg) is abundant in natural reserves and its alloys have a number of attractive properties 1,2 .
Specifically, Mg-alloys have high specific strength and specific stiffness, good damping and shock absorbing
capacity, high thermal conductivity, and strong electromagnetic shielding ability 1,2 . Thus, Mg alloys are widely
used for automotive, aerospace, and packaging applications. However, cold processing of Mg alloys is challenging
because Mg has a hexagonal close-packed (HCP) lattice with limited slip systems, making their deformation at
low temperature difficult. Another limiting factor that restricts the use of Mg alloys is their low thermal stability
leading to deterioration in mechanical properties at high temperatures. The melting temperature of Mg17Al12
phase in currently used Mg alloys (AZ and AM series) is ~735 K. In a number of structural applications, it is
desirable to have high strength and superior corrosion resistance.

Microalloying has been actively pursued to enhance the mechanical properties of Mg-alloys. Certain
microalloying elements form strengthening phases in the α -Mg matrix or at the grain boundaries, resulting in
solid-solution strengthening and/or precipitation strengthening. These secondary strengthening phases, formed
through microalloying, can assist in retaining a high dislocation density in the alloy by promoting the multiplication of dislocations and by pinning them, thereby improving the mechanical properties of Mg-alloys 3,4 .
Previous research has shown that the addition of Si or Sn in magnesium alloys led to the formation of thermally
stable and high-hardness Mg2Si or Mg2Sn phases, and thus improved the mechanical properties of Mg alloys
at room and high temperatures 5–8 . We selected Sn instead of Si as one of the alloying elements considering the
advantages of Mg2Sn phase and disadvantages of Mg2Si phase. The Mg2Sn phase has a high melting temperature
of 1051 K, which is significantly higher than 735 K of Mg17Al12 phase in the currently used AZ series of Mg alloys.
Additionally, the Mg2Sn phase has a high hardness of 119 HV. The high melting temperature and high hardness
of Mg2Sn phase makes it an excellent strengthening phase for enhancing mechanical properties and thermal
stability 9–12 . In contrast, the Mg2Si phase has a strong tendency to coarsen grains in as-cast Mg-alloys, thereby

1School of Materials Science and Engineering, Northeastern University, Shenyang 110819, P.R. China. 2State Key
Laboratory of Advanced Processing and Recycling of Non-ferrous Metals, Lanzhou University of Technology,
Lanzhou 730050, P.R. China. 3 Department of Metallurgical, Materials and Biomedical Engineering, University of
Texas at El Paso, TX 79968, USA. Correspondence and requests for materials should be addressed to Y.F.S. (email:
[shenyf@smm.neu.edu.cn)](mailto:shenyf@smm.neu.edu.cn)

Figure 1. Schematic illustration of a rheo-rolling process in this study.

decreasing strength, reducing casting ability of the alloys, and increasing their brittleness at room temperature.
In addition to Sn, Mn is also a beneficial element from the perspective of solid solution strengthening and grain
refinement 13,14 . Moreover, Bursik _et al._ demonstrated good creep resistance of Mg- _x_ Sn-1Mn ( _x_ = 3 and 5 wt.%)
alloys 15 . Shi and Huang _et al._ reported new relationship between the Mg2Sn phase and the α -Mg matrix in the
Mg-Sn-Mn alloy 16,17 .

Rare earth elements play an important role in governing the ultimate properties of Mg alloys. For example,
Wei _et al._ studied the creep properties of Mg-Sn-La alloys at high temperatures and observed that Mg– _x_ Sn–2La
( _x_ = 5, 6.5 and 8.5 wt.%) exhibits superior creep properties at high temperatures than Mg-5Sn (wt.%) alloy at
473 K and 25–35 MPa. The main reason for this observation was the presence of rare-earth strengthening phase
observed in Mg– _x_ Sn–2La ( _x_ = 5, 6.5 and 8.5 wt.%) alloy 11 . Although La is a beneficial alloying element, the influence of La on the microstructure and mechanical properties of Mg2Sn and other phases in Mg-3Sn-1Mn- _x_ La
(wt.%) alloy, and strengthening mechanisms remain largely unexplored.

Considering that cold processing of Mg alloys is difficult, we explored a novel semi-solid processing, specifically, continuous rheo-rolling, to produce Mg-3Sn-1Mn- _x_ La (wt.%) alloy and improve the ability of the alloy to
deform. Semi-solid processing has recently attracted significant attention to process magnesium-based alloys 18 .
However, extensive studies are required to translate this novel process to industrial applications. Continuous
rheo-rolling is a highly efficient semi-solid processing method in which a semi-solid metal composed of a liquid phase and a spherical solid phase is directly rolled following melting. In rheo-rolling, multiple traditional
solid processing steps, including ingot casting, solidification, re-heating, and rolling, are integrated into one process, which makes it cost-effective and energy-efficient process. Moreover, rheo-rolling has a higher processing speed for non-ferrous metals than liquid metal roll casting. Using continuous rheo-rolling, Haga (Osaka
Institute of Technology, Japan) produced A356 aluminum (Al) alloy plates with superior mechanical properties
(tensile strength of 270 MPa) compared to A5052-H34, A6063-T4 and T6 19 . Continuous rheo-rolling effectively
addresses the problem of poor deformability of Mg-alloys at room temperature. In this study, rheo-rolling processing with a novel shearing/vibration device for semi-solid metals was used to produce Mg-3Sn-1Mn (wt.%)
alloy plates to improve the microstructure and properties of the alloy 20 .

The objective of the study described here is to process Mg-3Sn-1Mn- _x_ La (wt.%) alloy plates with La concentration in the range of 0.2 to 1.4 wt.% using continuous rheo-rolling process, and elucidate the effect of La on the
microstructure and mechanical properties of Mg-3Sn-1Mn- _x_ La (wt.%) alloy plates that has not been previously
explored.

Experimental Procedure
A self-designed continuous rheo-rolling experimental apparatus was used to conduct the experiments 20 . The
roller diameter was 400 mm, the cross-sectional area of the prepared alloy plates was 4 mm × 160 mm, and
the maximum processing rate was 22 m/min. Figure 1 shows a schematic configuration of the equipment used
in this study 20 . A molten alloy was cast onto the vibrating slope plate to form a high-quality semi-solid metal
slurry via flow shear and vibration effects. This semi-solid metal slurry entered directly into the bottom of the
width-restricted roll for rheo-rolling. The process has two main advantages: (i) the temperature of the semisolid
slurry is significantly lower than the melt in conventional roll casting, resulting in short solidification time and
consequently very high rolling speed for the semi-solid alloy; and (ii) the process is expected to be developed as
a high-speed semi-solid roll-casting technique. Thus, using this approach, the mechanical properties of the strip
can be improved through tailoring of the microstructure.

The Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys used in this study were prepared using 99.95 wt.%
pure Mg, 99.95 wt.% pure Sn, Mg-25La (wt.%) alloy, and Mg-4.38Mn wt.% alloy. The nominal chemical composition (in wt.%) of the alloy was Mg-3% Sn-1% Mn-(0.2, 0.6, 1.0, 1.4%) La, with traces of 0.01% Si, 0.05% Cu,
0.01% Ni, and 0.01% Fe. A resistance furnace (3 kW, SG2-3-9, Shenyang General Furnace Manufacturing Co., Ltd,
China) was used to melt Mg alloys. The Ar gas was pumped into the resistance furnace when the temperature of
the furnace approached 673–773 K at a pressure of 1.5 MPa and flow rate of 5 l/min. After replacement of air with
argon inside the furnace, the magnesium ingots were placed inside the furnace and the temperature was increased

Figure 2. XRD patterns for the Mg-3Sn-1Mn- _x_ La alloys with different La addition: ( a ) 0.0 La; ( b ) 0.2 La; ( c ) 0.6 La;
( d ) 1.0 La; ( e ) 1.4 La. Each phase indicated by different symbols.

to 973–1003 K. Preheated and dried Sn metal, Mg-25La (wt.%) alloy, and Mn were added to the molten mixture,
and the temperature was increased and held at 1023 K for 20 min. Hexachloroethane was then used for degassing
and skimming of slag. Finally, Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloy plates were prepared by
casting under Ar-shielded atmosphere by continuous rheo-rolling at 943 K with a roller speed of 0.052 m·s −1, and
a flow rate of 15 l/min for cooling water 20 .

Samples of Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys of dimensions of 15 mm × 15 mm × 10 mm
and polished using standard metallographic procedure. X-ray diffraction (XRD; X’Pert, PANalytical B.V., Almelo,
Holland) was used to analyze precipitates in the Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys. Samples
with different La concentrations were first polished and etched using a solution consisting of 13 vol.% HCl,
47 vol.% C2H5OH, and 40 vol.% H2O at room temperature for 0.2 s, followed by scanning electron microscopy
(SEM; SSX-550, Shimadzu, Kyoto, Japan) to study the distribution of each element in the matrix. Samples with
different La concentrations were processed into Φ 3 mm × 0.5 mm discs using a spark-cutting machine (DK7740,
Precision Machinery Co., Ltd, China); the discs were then ground to a thickness of 80 μm and further thinned
using a precision ion polishing System (Gatan 691, USA). The microstructure and precipitate phase in the alloy
was analyzed using high-resolution transmission electron microscopy (HRTEM, Tecnai G 2 F20, FEI, Oregon,
USA). Uniaxial tensile tests were performed on a MTS 810 mechanical properties testing system (MTS, USA) at
a constant strain rate of 5 × 10 −3 s −1 at room temperature. A MTS LX300 laser extensometer was used to calibrate
and measure the sample strain on tensile loading. For each condition, three tests were performed to obtain the
average mechanical property data. After tensile tests, the alloy with the best mechanical properties was selected to
study the deformed microstructure by HRTEM. The optimal Mg-3Sn-1Mn- _x_ La (wt.%) alloy plate was deformed
to 2% elongation, and specimens were cut from the gage of the deformed samples, to fundamentally understand
the impact of precipitate phase on dislocation movement via HRTEM.

Results
Microstructure of Mg-3Sn-1Mn-xLa alloys. Figure 2 shows the effect of La concentration on precipitate
formation in Mg-3Sn-1Mn- _x_ La (wt.%) alloy plates as studied by X-ray diffraction for different La concentrations.
It can be seen that α -Mg and Mg2Sn were the two main phases in Mg-3Sn-1Mn-0.2La (wt.%) alloy (curve (b)).
However, the diffraction peaks of Mg2Sn phase at (111), (200), (222) and (513) were weaker than those observed
in Mg-3Sn-1Mn (wt.%) alloy. As shown in curve (c) in Fig. 2, when the La concentration was increased to
0.6 wt.%, diffraction peak intensities associated with the Mg2Sn phase at (111), (200), (222) and (513) were further
decreased. The Mg17La2 phase emerged at (312) and (116) and the La5Sn3 phase emerged at (330). The diffraction
peaks corresponding to La5Sn3 phase at (111) and (930) overlapped with the α -Mg phase at (100) and (201),
respectively, while the diffraction peak at (642) overlapped with the diffraction peaks of Mg2Sn phase at (513).
As the La concentration was increased to 1.0 wt.% (curve (d)), the diffraction peak intensities corresponding to
Mg2Sn phase at (111), (200), (222) and (513) was further decreased. A new diffraction peak emerged at (412)
position and was identified as Mg17La2 phase, suggesting a gradual increase in the volume fraction of Mg17La2
phase. Meanwhile, the diffraction peak intensity at (330) was also increased for the La5Sn3 phase. As the La
concentration was increased to 1.4 wt.%, the diffraction peak intensities of the Mg2Sn phase at (200), (222) and
(513) were very weak as shown in curve (e) in Fig. 2. The intensities were increased for Mg17La2 phase ((312) and
(116) peaks) and La5Sn3 phase ((330) peak). New diffraction peaks emerged at (500) and (006) were identified as
Mg17La2 phase.

Figure 3a–c are SEM micrographs and the associated results of energy dispersive X-ray spectrometer (EDS)
analysis of α -Mg grain boundaries, labeled as 1–3 in Table 1. These results indicate that in Mg-3Sn-1Mn-0.2La
(wt.%) alloy, the compounds formed at the grain boundaries were primarily composed of Mg and Sn with a ratio

Figure 3. SEM observations show the morphologies of ( a ) Mg-3Sn-1Mn-0.2La, ( b ) Mg-3Sn-1Mn-0.6La and
( c ) Mg-3Sn-1Mn-1.4La alloys. Chemical compositions of regions 1, 2 and 3 detected by EDS and listed in
Table 1.

of ~2:1, based on atomic %. Based on XRD and EDS analyses, the compound formed at α -Mg grain boundaries
was determined to be Mg2Sn phase, which was confirmed by TEM studies (Fig. 4a–c). The associated results of
energy dispersive X-ray spectrometer (EDS) analysis at the α -Mg grain boundaries are labeled as 4–6 (Table 1).
Only a short, rod-like Mg2Sn phase was observed, with an average length of 100 ± 5 nm and an average width of
45 ± 2 nm. XRD and EDS results indicated that no La-containing phase precipitated in the Mg-3Sn-1Mn-0.2La
(wt.%) alloy, and majority of La was present in solid solution in the α -Mg matrix.

EDS analysis revealed that the chemical composition was 56.5Mg-26.5Sn-17.0La (wt.%) for the plate-shaped
compound at the α -Mg grain boundary of Mg-3Sn-1Mn-0.6La alloy (No. 3 in Table 1). The TEM observations, suggested that this new phase was present as plate-like at α -Mg grain boundary, with an average length
of 380 ± 10 nm and an average width of 110 ± 5 nm (Fig. 5a). This plate-shaped compound had a Mg:Sn:La ratio
of ~66:26:7 (at.%), as determined from EDS analysis (No. 7 in Table 1). As shown in Fig. 5b, the average length
of the plate-shaped compound at the α -Mg grain boundary of Mg-3Sn-1Mn-1.0La (wt.%) plates approached
~560 ± 20 nm and an average width of 90 ± 5 nm, indicating a significant increase in volume fraction, and the

No. In alloy Element wt.% at.%

1 Mg-3Sn-1Mn-0.2 La

2 Mg-3Sn-1Mn-0.6 La

3 Mg-3Sn-1Mn-1.4 La

4 Mg-3Sn-1Mn-0.2 La

5 Mg-3Sn-1Mn-1.0 La

6 Mg-3Sn-1Mn-1.4 La

7 Mg-3Sn-1Mn-0.6 La

8 Mg-3Sn-1Mn-1.0 La

9 Mg-3Sn-1Mn-1.4 La

Mg 31.7 65.1

Sn 68.3 34.9

Mg 53.9 85.6

Sn 33.9 11.0

La 12.2 3.4

Mg 56.5 87.1

Sn 26.5 8.4

La 17.0 4.6

Mg 40.3 76.7

Sn 59.7 23.3

Mg 49.5 82.7

Sn 50.5 17.3

Mg 54. 6 85.4

Sn 45.4 14.6

Mg 27.9 66.2

Sn 54.4 26.4

La 17.7 7.4

Mg 35.8 73.8

Sn 47.9 20.3

La 16.3 5.9

Mg 34.8 73.1

Sn 48.1 20.7

La 17.1 6.3

Table 1. Chemical compositions of different regions in the Mg-3Sn-1Mn- _x_ La alloys obtained by EDS
analysis. Numbers represent the different positions in Figs 3, 4 and 5, respectively.

compound appeared to be evenly distributed at the α -Mg grain boundary. The related EDS analysis is listed
in Table 1 (labeled as 8). This plate-shaped compound grew perpendicular to the α -Mg grain boundary and
extended toward the inside of the matrix, preventing the α -Mg grain boundary from sliding (Figs 5 and 6),
and thereby potentially increases the strength of the alloy. In addition, the refinement of the Mg2Sn phase was
beneficial in improving the mechanical properties of Mg-Sn-Mn alloy 17 . This aspect is supported by the observation that a spherodized Mg2Sn phase of ~50 ± 2 nm in diameter was formed and evenly distributed between
the plate-shaped compounds (the inset in Fig. 5b). The volume fraction of compound increased in comparison
to the other two alloys (Fig. 3 and No. 3 in Table 1). The Mg2Sn phase continued to be intragranular precipitate,
and variation in morphology and distribution were not significant, as shown in Fig. 4c. However, the quantity
of the plate-shaped compounds at the α -Mg grain boundary was increased. The average length increased to
2300 ± 50 nm, whilst the average width decreased to 70 ± 5 nm (Fig. 5c).
Figure 6a,b are the morphologies of the plate-shaped compound observed along the zonal direction of

[10,11]Mg, and Fig. 6c,d show the diffraction patterns of these plate-shaped compounds that overlapped with
the surrounding α -Mg matrix. Two systems of periodic spots can be seen in Fig. 6c. One set of spots indicated
by red lines reveal R11 = 3.5, R12 = 7.4, along with an angle of 74° between R11 and R12. Therefore, these spots are
indexed as La5Sn3 phase (body-centered tetragonal, BCT, _a_ = _b_ = 1.2740 nm, _c_ = 0.6343 nm) according to the

[122]La5Sn3 zone axis. The other set of spots indicated by yellow lines reveal R21 = 1.5, R22 = 2.2, and an angle of
67° between R21 and R22. These spots are indexed according to the [11–23]Mg17La2 zone axis of the Mg17La2 (HCP,
_a_ = _b_ = 1.0360 nm, _c_ = 1.0240 nm) phase (Fig. 6c). Moreover, another set of relatively regular spots were observed
in Fig. 6d, showing R31 = 1.6, R32 = 2.1 as well as an angle of 106° between R31 and R32. These spots are indexed
as Mg2Sn (face-centered cubic, FCC, _a_ = _b_ = _c_ = 0.6759 nm) phase according to the [433]Mg2Sn zone axis. Thus, it
was confirmed that this plate-shaped compound was composed of La5Sn3, Mg2Sn and Mg17La2 phases, which is
consistent with the XRD analysis presented in Fig. 2. This new-type of composite structure was first observed in
this study and has not been previously reported 8–13 .

With increasing La concentration in the range of 0.2–1.4 wt.%, the intragranular Mg2Sn phase was gradually
refined, spherodized, and uniformly distributed. The average length of the plate-shaped compound (La5Sn3 and
Mg17La2 phases) was gradually increased, accompanied by decreasing width and average length of Mg2Sn phase
(Fig. 7).

Mechanical properties of Mg-3Sn-1Mn-xLa alloys. Engineering stress-strain plots of Mg-3Sn1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys tested at room temperature are presented in Fig. 8a. The Mg-3Sn1Mn (wt.%) alloy showed no yield plateau during tensile straining. However, on the addition of La, yield plateau
was observed for Mg-3Sn-1Mn- _x_ La (wt.%) alloys during tensile tests, which is different from the deformation
characteristics of the reported Mg-alloys 4 . Figure 8b summaries the influence of La concentration on tensile stress
and elongation of Mg-3Sn-1Mn- _x_ La (wt.%) alloys. With increased La concentration, the tensile strength and

Figure 4. TEM images show the morphologies of ( a ) Mg-3Sn-1Mn-0.2La, ( b ) Mg-3Sn-1Mn-1.0La and ( c ) Mg3Sn-1Mn-1.4La alloys observed along [0001]Mg zonal axis. Chemical compositions of regions 4, 5 and 6 by EDS
are listed in Table 1.

elongation of the alloys was first increased and then decreased, the peak values were achieved at 1.0 wt.% La. The
Mg-3Sn-1Mn-1.0La (wt.%) alloy plate exhibited a tensile strength of 230 ± 10 MPa and elongation of 7.5 ± 0.2%.
These values are 29% and 32% higher than the tensile strength (175 ± 5 MPa) and elongation (5.6 ± 0.1%) of
Mg-3Sn-1Mn (wt.%) alloy, and are respectively 37% and 89% higher than the tensile strength and elongation
of Mg-3Sn-1Mn-0.87Ce (wt.%) alloy 13 . The small but consistently observe improvement in elongation of ~2%
is encouraging because Mg element is an intrinsic brittle metal. The symmetry of the hexagonal close-packed
(HCP) crystal structure has limited number of independent slip systems, resulting in poor ductility at room
temperature 21 . Moreover, the melting points of precipitates are higher than pure Mg. For example, La5Sn3such
has a melting point of 1500 °C, whilst that of Mg17La2 is 672 °C. Thus, the stability of mechanical properties can be
improved by the addition of La to Mg alloys.

Discussion
Mechanism of microstructure formation. The difference in electronegativity of alloying elements determines their ability to form compounds. The greater the difference in electronegativity, the larger the binding force

Figure 5. TEM images show the morphologies of ( a ) Mg-3Sn-1Mn-0.6La, ( b ) Mg-3Sn-1Mn-1.0La and ( c ) Mg3Sn-1Mn-1.4La alloys close to grain boundaries. The incideent beam was aligned to [0001] zonal axis of α -Mg
matrix. Chemical compositions of regions 7, 8 and 9 by EDS are listed in Table 1.

between these elements, thus making them more likely to form a compound 13,22 . Table 2 summarizes the electronegativity difference between Mg, Sn, La and Mn. The maximum difference in electronegativity is between La
and Sn, followed by Mg and Sn 13,22 . The solid solubility of La in the α -Mg matrix is 0.14 wt.% 23, and thus, majority
of La is dissolved within the α -Mg matrix, when 0.2 wt.% La was added to the alloy. In the Mg-3Sn-1Mn-0.2La
(wt.%) alloy, La-containing phases did not form because of the fast cooling rate of the vibration plate during continuous rheo-rolling and the rapid solidification rate of the alloy 20 . At room temperature, the solid solubility of
Sn in α -Mg matrix is 0.17 wt.%, and there was relatively more Sn in Mg-3Sn-1Mn- _x_ La (wt.%) alloys, which was
beneficial for the formation of the Mg2Sn phase. Zhou _et al._ calculated that the heat needed for Mg2Sn formation
and the binding energy for the Mg2Sn phase was − 20.82 kJ/mol and 251.83 kJ/mol, respectively, demonstrating
the stability of Mg2Sn phase 24 . Hence, the Mg-3Sn-1Mn-0.2La (wt.%) alloy was primarily composed of α -Mg and
Mg2Sn phases. La and Sn combined with each other (Table 2), according to the qualitative thermokinetic criteria
theory suggested by Mendis _et al._ 25 .

In addition to the microalloying ability, La can also facilitate the nucleation of Sn-containing phases 25 . Thus,
with increase in La concentration, a significant amount of La was homogeneously distributed within the matrix,

Figure 6. ( a ) Bright field and ( b ) dark field TEM images as well as diffraction patterns ( c,d ) of plate-shaped
compound.

Figure 7. Effect of La concentration on the type and size of precipitates in Mg-3Sn-1Mn-xLa (wt.%) alloys.

as indicated by SEM observations, which facilitates an uniform distribution of Sn phase near the grain boundaries
and the nucleation of Mg2Sn phase (Fig. 9a–c). During the growth of Mg2Sn phase, the surrounding La atoms
segregate on the surface of initial Mg2Sn phase, thus increasing the surface energy and making it very difficult for
surface atoms to continuously diffuse into the inner Mg2Sn phase, which hinders further growth of Mg2Sn phase,
resulting in the gradual refinement and spherodization of Mg2Sn phase. As a result, the Mg2Sn phase becomes
smaller and the aspect ratio is close to 1 with increase in La concentration (Fig. 4).

During the solidification of the alloy, as the solute concentration was high to form intermetallic compounds,
the phase with the highest melting point will be the first to form. Then, as the temperature of the molten alloy
decreases, eutectic reactions occur among the remaining alloying elements and phases with low melting point
start to form 26 . Because of the large electronegativity difference between La and Sn (Table 2), and higher melting
point of La5Sn3 phase (1773 K) than Mg2Sn (1043 K) and Mg17La2 phases (945 K), La5Sn3 phase first nucleated and
grew at the α -Mg grain boundary, when the La concentration was 0.6 wt.% (Fig. 10a,b). Idbenali _et al._ showed that

Figure 8. ( a ) Engineering stress-strain curves of Mg-3Sn-1Mn- _x_ La alloys at room temperature. ( b ) Evolution
of tensile stress and strain with the variation of La concentrations in Mg-3Sn-1Mn- _x_ La alloys.

Mg (1.31) Sn (1.96) La (1.10) Mn (1.55)

Mg (1.31) 0 0.65 0.21 0.24

Sn (1.96) 0.65 0 0.86 0.41

La (1.10) 0.21 0.86 0 0.45

Mn (1.55) 0.24 0.41 0.45 0

Table 2. Differences of electronegativity value between Mg, Sn, La and Mn.

La5Sn3 phase was stable at room temperature 27 . The La5Sn3 phase contained few Sn atoms and no Mg atoms and
grew perpendicular to the α -Mg grain boundary, resulting from eutectic transformation during the final solidification. Thus, during the formation of La5Sn3 phase at the α -Mg grain boundary, Mg and Sn atoms were constantly expelled and accumulated at the solidification interface, such that the nucleation of Mg2Sn phase occurred.
The formation of La5Sn3 phase provided a site for the formation of Mg2Sn phase (Fig. 10c). As the Mg2Sn phase
adhered to the surface of the La5Sn3 phase and nucleation started, its surface energy was decreased; therefore,
nucleation occurred at lower degree of undercooling (Fig. 10d). Additionally, since the electronegativity difference between Mg and Sn is greater than between Mg and La, and the melting point of the Mg2Sn phase is higher
than Mg17La2 phase, thus, the Mg2Sn phase nucleated on La5Sn3 phase, prior to the nucleation of Mg17La2 phase.
With nucleation and growth of Mg2Sn phase, Mg and La atoms were expelled and accumulated at the liquid-solid
interface, providing constituents for the formation of the Mg17La2 phase, as well as the adherent points for nucleation of the Mg17La2 phase, thus facilitating the formation of the Mg17La2 phase (Fig. 10e). Therefore, at the
α -Mg grain boundary, La5Sn3, Mg2Sn and Mg17La2 phases nucleated and grew alternately, forming a plate-shaped
compound comprising of three phases, confirmed by HRTEM (Fig. 10) and XRD and EDS analyses (Fig. 2 and
Table 1).

As the La concentration increased, more La5Sn3 and Mg17La2 were gradually formed and plate-shaped
compounds comprising of La5Sn3, Mg2Sn, and Mg17La2 phases at the α -Mg grain boundary. In Mg-La alloys,
higher concentration of La increases the cohesive energy of Mg-La compound and α -Mg grain stability, which is
favorable for increasing the stability of La-containing phases 28 . Thus, the stability of La5Sn3 and Mg17La2 phases

Figure 9. SEM image ( a ), Sn ( b ) and La ( c ) distribution maps of Mg-3Sn-1Mn-1.0La (wt.%) alloys.

increased with increasing La concentration, promoting increase in La5Sn3 phase. The formation of La5Sn3 phase
consumed majority of Sn atoms in the liquid phase, resulting in gradual decrease in Mg2Sn concentration.

Effects of microstructure on mechanical properties of alloys. It can be seen from Fig. 8 that after the
addition of La, the Mg-3Sn-1Mn-xLa alloy showed a yield plateau during stretching, which is seldom observed
in Mg alloys 4 . The yield plateau is mainly due to the pinning effect of the precipitates such as La5Sn3, Mg2Sn, and
Mg17La2 on dislocations. As dislocations are pinned by the precipitates, higher stress is required for dislocations to
escape the blockage of the precipitates and move, thus generating the upper yield point. Once dislocations eventually overcome the pinning force, they move and the stress decreases, generating the lower yield point. Several
studies have shown that rare earth atoms can effectively impede dislocation movement 4,29,30 .

Figure 10. High-resolution TEM images ( a,b ) show the morphologies of the plate compound and α -Mg
matrix. Schematic diagram of plate-shaped compound formation: ( c ) La5Sn3 phase nucleation; ( d ) Mg2Sn phase
adheres to La5Sn3 phase for nucleation; ( e ) Mg17La2 adheres to Mg2Sn for nucleation.

In Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys, the dimension, size and distribution of Mg2Sn
phase plays an important role in dictating the ultimate mechanical properties of the alloy 17,31 . Figure 11 shows a
HRTEM image and Fourier transformation of Mg2Sn phase and α -Mg matrix. The Mg2Sn phase were coherent
with α -Mg matrix along the [1–100]Mg direction, with an interplanar spacing of 0.26 nm for the [000–2]Mg plane
of α -Mg matrix and 0.24 nm for the [220]Mg2Sn plane of Mg2Sn phase. The lattice mismatch between the Mg2Sn
phase and α -Mg matrix along with the resulting stress field can influence the deformation of alloy by restricting
their dislocation movement. The degree of mismatch is defined by the following equation 32,33 :

_δ_ =

2 a _γ_ ′ - a

a _γ_ ′ + a

a _γ_ ′ + a _γ_ (1)

_γ_ ′ - a _γ_

_γ_ ′ + a _γ_

′

where aγ and aγ′ are to the interplanar spacing of γ and γ′ phase, respectively. The Mg2Sn phase and α -Mg matrix
have a small degree (8.0%) of mismatch and low interfacial strain energy between (220)Mg2Sn and (0002)Mg lattices.
Their interface is relatively stable and less likely to allow nucleation or initiation of microcracks during deformation, suggesting that the Mg2Sn phase is helpful in improving the mechanical properties of Mg-3Sn-1Mn- _x_ La
( _x_ = 0.2, 0.6, 1.0 and 1.4 wt.%) alloys. Additionally, there is an angle of 5.5° between the (220)Mg2Sn plane of the
Mg2Sn phase and the (0001)Mg plane of the α -Mg matrix. Since the (0001)Mg plane is the glide plane of dislocations in Mg alloys 34, the formation of Mg2Sn phase can effectively impede dislocations from the basal slip, leading
to an increase in the strength of the alloys.

After deformation to a strain of 2%, a high density of dislocations can be observed around the Mg2Sn phase in
the Mg-3Sn-1Mn-1.0La alloy (Fig. 11), suggesting that the Mg2Sn phase had a pinning effect on the movement of
dislocations. In fact, it is reported that the Mg2Sn phase is a hard phase in Mg-3Sn-1Mn- _x_ La ( _x_ = 0.2, 0.6, 1.0 and
1.4 wt.%) alloys with a microhardness of 1.19 GPa 7–9 . When the dislocations move to the region near the Mg2Sn
particles, they indicated a tendency to bypass the Mg2Sn phase (Fig. 12a), leading to Orowan strengthening 35 . A
similar scenario has been reported by Sasaki _et al._ 36 . On the other hand, the Mg2Sn phase was gradually refined,
spherodized, and more uniformly distributed with increased La concentration (Figs 4 and 7), leading to increase
in the pinning effect of Mg2Sn phase on dislocations slip 17 . For example, the length of Mg2Sn phase decreased
from 100 nm to 50 nm with increased La addition from 0.2% to 1.4%, exhibiting equiaxial morphology.

Based on the well-known Orowan mechanism, the strength increment due to precipitation strengthening,
_σ_ prec., is given by equation (2) 35 :

Figure 11. High-resolution TEM images ( a,b ) show the morphologies of the plate compound and α -Mg
matrix. The corresponding diffractogram ( c,d ) obtained by fast Fourier Transform (FFT).

_σ_

0 8. _MGb_
_prec_ . = _λ_ (2)

where _M_ is the Taylor factor, _G_ is the shear modulus, _b_ is the Burgers vector and _λ_ is the average spacing between
neighboring particles. Apparently, a decrease in both particle size and the spacing of adjacent precipitates not only
increases the stress required for dislocation movement, but also dislocation density, leading to increased strength
of the studied alloys. With increase in La concentration to 1.0 wt.%, a plate-shaped compound composed of
La5Sn3, Mg2Sn and Mg17La2 phases formed at the α -Mg grain boundary of the Mg-3Sn-1Mn-1.0La (wt.%) alloy.
Despite increased average length to 560 ± 10 nm, the width of the plate compounds reduced to 90 ± 5 nm, accompanied by a decrease in length of Mg2Sn particles to 50 nm. Following equation (2), the strength associated with
precipitation strengthening should increase because of reduced spacings between plate-shaped compounds and
spherical Mg2Sn particles. This deduction was supported by tensile tests, as indicated in Fig. 8. Grain boundary
sliding plays a significant role during the plastic deformation of the alloy, therefore, the morphology of the precipitates at α -Mg grain boundary and the energy of α -Mg grain boundary are important factors in governing the
strain of the alloy 37 . The plate-shaped composite was characterized by HRTEM (Figs 10 and 11) and the degree of
mismatch was 4.6% according to equation (1). This value means that the interface has a lower strain energy and
this kind of interface is more stable, less likely to initiate nucleation and growth of microcracks during deformation. Moreover, this plate-shaped compound is formed near the α -Mg grain boundary and grows perpendicular
to the boundary and toward inside of the α -Mg matrix, by pinning the α -Mg grain boundary and impede the
sliding of α -Mg grain boundary (Figs 5, 6, 10 and 11). As the dislocations move to a nearby location in the vicinity
of the plate-shaped compound, they pile up because of impeding effect of the compound (Fig. 12), leading to an
increase in the strength of the alloy.

As the La concentration approached 1.4 wt.%, more plate-shaped compounds were formed and gradually
became thinner, with average thickness of 70 ± 5 nm and significantly increased average length of 2300 ± 50 nm.
According to equation (2), the stress increment derived from precipitation strengthening should increase because
the thickness of plate-shaped compounds decreased (Figs 5c and 6). However, Fig. 8 shows that both tensile
strength and strain decreased with increasing La content from 1.0% to 1.4%. The main reason must be related to
the high degree of segregation of the plate compounds (Figs 3c and 5c), though the size of Mg2Sn particles still

Figure 12. TEM images reveal that the pile-up effect of precipitates to dislocations in the Mg-3Sn-1Mn-
1.0La (wt.%) alloy after tension with 2% engineering strain at room temperature. ( a,b ) show the pinned
dislocations (triangle) by the spherical Mg2Sn phase, whilst ( c ) indicates high density of dislocations impeded
by the platelike compound (arrows).

remained constant as small as ~50 nm, in comparison to that of Mg-3Sn-1Mn-1.0La (wt.%) alloy. As a result, the
total pinning effect of the precipitates on the α -Mg grain boundary was decreased due to the high degree of segregation of plate-shaped compounds, despite similar dimension of Mg2Sn particles, leading to a relatively weak
hardening effect compared to the alloy containing 1.0 wt.% La.

A power-law hardening equation can be used to describe the flow strength of metal materials, as follows 38 :

_σ_ = _K_ 1 + _K_ 2 _ε_ (3)

where _σ_ is the flow stress, _ɛ_ is the strain, n is the work hardening exponent, _K_ 1 represents the initial yield strength
of the materials and _K_ 2 represents the increment in strength due to work hardening. According to equation (3),
instability necking is activated, when _ɛ_ u = n (uniform elongation) during uniaxial tension of sheet specimens.
Referring to Fig. 8a, it is evident that the Mg-3Sn-1Mn-1La alloy had the highest _n_ value among all the five alloys.

Thus, the decrease in strain of Mg-3Sn-1Mn-1.4La alloy must be associated with the localized necking resulted
from the high degree of segregation of plate-shaped compounds.

Conclusions
We have elucidated here the effect of La on the microstructure and properties of Mg-3Sn-1Mn-xLa ( _x_ = 0.2, 0.6,
1.0 and 1.4 wt.%) alloys produced by continuous rheo-rolling process. The major conclusions are as follows:

(a) A maximum 0.2 wt.% La was completely dissolved in α -Mg matrix to form a solid solution with precipitated

Mg2Sn phase, which was coherent with the α -Mg matrix along the [1–100]Mg zonal direction. The (220) plane
of the Mg2Sn phase and the (0001) plane of the α -Mg matrix formed a 5.5° angle. The Mg2Sn phase had a
pinning effect on dislocation slip.
(b) With increase in La content to 0.6 wt.%, the La5Sn3, Mg2Sn and Mg17La2 phases nucleated alternately to form a

new-type plate-shaped three-phase compound. This plate-shaped compound was coherent with α -Mg matrix
along the [10–1–2]Mg zonal direction, and grew perpendicular to the inside of α -Mg grain, producing pinning effect on the α -Mg grain boundaries and dislocations.
(c) At La content in the range of 0.2–1.4 wt.%, the Mg2Sn phase was gradually refined and spherodized in α -Mg

matrix. The length of the plate-shaped compound was gradually increased from 380 ± 10 nm to 2300 ± 50 nm,
and the width reduced from 110 ± 5 nm to 70 ± 5 nm. The tensile strength and elongation of the alloy gradually increased with increase in La content from 0.2–1.0 wt.% and then decreased on further increase in La
content from 1.0–1.4 wt.%, mainly associated with the segregation of plate-shaped compounds.
(d) At La content of 1.0 wt.%, the tensile strength and elongation of the alloy attained maximum. In comparison

with Mg-3Sn-1Mn (wt.%) alloy, the tensile strength and elongation increased by 29% and 32%, respectively.
In comparison with the Mg–3Sn–1Mn-0.87 Ce (wt.%) alloy, the tensile strength and elongation increased by
37% and 89%, respectively. The nanosized Mg2Sn particles and plate-shaped compounds played an important
role in improving the mechanical properties.

References

1. Qiu, D., Zhang, M. X., Taylor, J. A. & Kelly, P. M. A new approach to designing a grain refiner for Mg casting alloys and its use in
Mg-Y-based alloys. _Acta Mater_ . 57, 3052–3059 (2009).
2. Yamasaki, M., Hashimoto, K., Hagihara, K. & Kawamura, Y. Effect of multimodal microstructure evolution on mechanical
properties of Mg-Zn-Y extruded alloy. _Acta Mater_ . 59, 3646–3658 (2011).
3. Wang, J. F., Song, P. F., Huang, S. & Pan, F. S. High-strength and good-ductility Mg-RE-Zn-Mn magnesium alloy with long-period
stacking ordered phase. _Mater. Lett._ 93, 415–418 (2013).
4. Stanford, N., Atwell, D. & Barnett, M. R. The effect of Gd on the recrystallisation, texture and deformation behaviour of magnesiumbased alloys. _Acta Mater_ . 58, 6773–6783 (2010).
5. Poddar, P., Sahoo, K. L., Mukherjee, S. & Ray, A. K. Creep behaviour of Mg-8%Sn and Mg-8%Sn-3%Al-1%Si alloys. _Mater. Sci. Eng._
_A_ 545, 103–110 (2012).
6. Poddar, P. & Sahoo, K. L. Microstructure and mechanical properties of conventional cast and rheocast Mg-Sn based alloys. _Mater._
_Sci. Eng_ . _A_ 556, 891–905 (2012).
7. Kang, D. H., Park, S. S. & Kim, N. J. Development of creep resistant die cast Mg–Sn–Al–Si alloy. _Mater. Sci. Eng_ . _A_ 413–414, 555–560
(2005).
8. Nayyeri, G. & Mahmudi, R. Effects of Ca additions on the microstructural stability and mechanical properties of Mg-5%Sn alloy.
_Mater. Design_ 32, 1571–1576 (2011).
9. Liu, H. M., Chen, Y. G., Tang, Y. B., Wei, S. H. & Niu, G. Tensile and indentation creep behavior of Mg-5%Sn and Mg-5%Sn-2%Di
alloys. _Mater. Sci. Eng_ . _A_ 464, 124–128 (2007).
10. Yang, M. B., Cheng, L. & Pan, F. S. Comparison of as-cast microstructure, tensile and creep properties for Mg-3Sn-1Ca and Mg-3Sn2Ca magnesium alloys. _Trans. Nonferrous Met. Soc. China_ 20, 584–589 (2010).
11. Wei, S. H. _et al._ Compressive creep behavior of Mg-Sn-La alloys. _Mater. Sci. Eng. A_ 508, 59–63 (2009).
12. Liu, H. M., Chen, Y. G., Zhao, H. F., Wei, S. H. & Gao, W. Effects of strontium on microstructure and mechanical properties of as-cast
Mg-5 wt.%Sn alloy. _J. Alloys Compd._ 504, 345–350 (2010).
13. Pan, F. & Yang, M. Preliminary investigations about effects of Zr, Sc and Ce additions on as-cast microstructure and mechanical
properties of Mg-3Sn-1Mn (wt.%) magnesium alloy. _Mater. Sci. Eng. A_ 528, 4973–4981 (2011).
14. Masoumi, M., Hoseini, M. & Pekguleryuz, M. The influence of Ce on the microstructure and rolling texture of Mg-1%Mn alloy.
_Mater. Sci. Eng. A_ 528, 3122–3129 (2011).
15. Bursik, J. _et al._ Microstructure and mechanical properties of as-cast Mg-Sn-Ca and Mg-Sn-Mn alloys, Magnesium: Proceedings of
the 7th International Conference Magnesium Alloys and Their Applications (ed. Kainer, K. U.), Weinheim, Germany, 37–42 (2006).
16. Shi, Z. Z., Dai, F. Z. & Zhang, W. Z. Crystallography of Mg2Sn precipitates with two newly observed orientation relationships in an
Mg-Sn-Mn alloy. _Mater. Sci. Technol_ . 28, 411–414 (2012).
17. Huang, X. F. & Zhang, W. Z. Improved age-hardening behavior of Mg-Sn-Mn alloy by addition of Ag and Zn. _Mater. Sci. Eng. A_ 552,
211–221 (2012).
18. Flemings, M. C. Behavior of metal alloys in the semisolid state. _Mater. Trans. A_ 22, 269–293 (1991).
19. Haga, T. Semisolid strip casting using a twin roll caster equipped with a cooling slope. _J. Mater. Process Tech_ . 130–131, 558–561
(2002).
20. Guan, R. G. _et al._ Microstructure evolution and properties of Mg-3Sn-1Mn (wt%) alloy strip processed by semisolid rheo-rolling. _J._
_Mater. Process Tech_ . 212, 1430–1436 (2012).
21. Máthis, K., Gubicza, J. & Nam, N. H. Microstructure and mechanical behavior of AZ91 Mg alloy processed by equal channel angular
pressing. _J. Alloy. Comp_ . 394, 194–199 (2005).
22. Zhang, X. P. _et al._ Microstructure, tensile properties and compressive creep resistance of Mg-(5–8.5)%Sn-2%La alloys. _Trans._
_Nonferrous Met. Soc_ . _China_ 18, 299–305 (2008).
23. Nayeb-Hashemi, A. A. & Clark J. B. The La-Mg (Lanthanum-Magnesium) system. _Bulletin of Alloy Phase Diagrams_ 9, 172–178
(1988).
24. Zhou, D. W., Xu, S. H., Zhang, F. Q., Peng, P. & Liu, J. S. First-principle study on structural stability of Sn alloying MgZn2 phase and
Mg2Sn phase. _Chinese Journal of Nonferrous Metals_ 20, 914–922 (2010).
25. Mendis, C. L., Bettles, C. J., Gibson, M. A., Gorsse, S. & Hutchinson, C. R. Refinement of precipitate distributions in an agehardenable Mg-Sn alloy through microalloying. _Philos. Mag. Lett_ . 86, 443–456 (2006).

26. Xiao, W. L., Jia, S. S., Wang, J. L., Yang, J. & Wang, L. M. The influence of mischmetal and tin on the microstructure and mechanical
properties of Mg-6Zn-5Al-based alloys. _Acta Mater._ 56, 934–941 (2008).
27. Idbenali, M., Servant, C., Selhaoui, N. & Bouirden, L. A thermodynamic reassessment of the La-Sn system. _Calphad_ 33, 398–404
(2009).
28. Wang, Y. F. _et al._ First-principles study of structural stabilities and electronic characteristics of Mg-La intermetallic compounds.
_Comp. Mater. Sci_ . 41, 78–85 (2007).
29. Wu, L. Y. _et al._ The tensile properties at 448 K and the fracture behaviors under _in situ_ transmission electron microscope strain for
the Mg-6.0Gd-1.2Zn-0.15Y alloy. _Mater. Design_ 40, 199–204 (2012).
30. Hahn, G. T. A model for yielding with special reference to the yield-point phenomena of iron and related bcc metals. _Acta Metall_ .
10, 727–738 (1962).
31. Elsayed, F. R., Sasaki, T. T., Mendis, C. L., Ohkubo, T. & Hono, K. Compositional optimization of Mg–Sn–Al alloys for higher age
hardening response. _Mater. Sci. Eng. A_ 566, 22–29 (2013).
32. Dirand, L. _et al._ Measurement of the effective γ /γ′ lattice mismatch during high temperature creep of Ni-based single crystal
superalloy. _Mater. Charact_ . 77, 32–46 (2013).
33. Link, T., Epishin, A., Brückner, U. & Portella, P. Increase of misfit during creep of superalloys and its correlation with deformation.
_Acta Mater_ . 48, 1981–1994 (2000).
34. Sasaki, T. T., Oh-ishi, K., Ohkubo, T. & Hono, K. Enhanced age hardening response by the addition of Zn in Mg-Sn alloys. _Scripta_
_Mater_ . 55, 251–254 (2006).
35. Orowan, E. In: Cohen, M. (Ed.), _Dislocations in metals_, AIME, New York, 31–32 (1954).
36. Sasaki, T. T., Oh-ishi, K., Ohkubo, T. & Hono, K. Effect of double aging and microalloying on the age hardening behavior of a MgSn-Zn alloy. _Mater. Sci. Eng. A_ 530, 1–8 (2011).
37. Kim, B. H., Park, K. C., Park, Y. H. & Park, I. M. Investigations of the properties of Mg-4Al-2Sn-1Ca-xCe alloys. _Mater. Sci. Eng. A_
527, 6372–6377 (2010).
38. Misra, A., Zhang, X., Hammon, D. & Hoagland, R. G. Work hardening in rolled nanolayered metallic composites. _Acta Mater_ . 53,
221–226 (2005).

Acknowledgements
The research was supported by the National Natural Science Foundation of China (Grant Nos 51574079,
51474063), NSAF (Grant no. U1430132), and the National Science Foundation for Outstanding Young
Scholars of China under grant no. 51222405. This project is also supported by the fund of the State Key
Laboratory of Advanced Processing and Recycling of Non-ferrous Metals, Lanzhou University of Technology
(SKLAB02015005).

Author Contributions
R.G.G. designed the research plan together with Y.F.S. prepared figures and wrote the manuscript. Z.Y.Z.
conducted experiments and characterization of the alloys. R.D.K.M. collaborated in this study in terms of
discussion and useful suggestions. All authors reviewed the manuscript.

Additional Information
Competing financial interests: The authors declare no competing financial interests.

How to cite this article : Guan, R.G. _et al._ Nanoscale precipitates strengthened lanthanum-bearing Mg-3Sn1Mn alloys through continuous rheo-rolling. _Sci. Rep._ 6, 23154; doi: 10.1038/srep23154 (2016).

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